U.S. patent number 3,736,880 [Application Number 05/219,713] was granted by the patent office on 1973-06-05 for feedback control circuit for magnetic suspension and propulsion system.
This patent grant is currently assigned to Rohr Industries Inc.. Invention is credited to James A. Ross.
United States Patent |
3,736,880 |
Ross |
June 5, 1973 |
FEEDBACK CONTROL CIRCUIT FOR MAGNETIC SUSPENSION AND PROPULSION
SYSTEM
Abstract
A linear motor uses the same magnetic flux for suspension and
propulsion of a high speed tracked vehicle and operates below a
support rail without physical contact therewith. Displacement and
inertial sensors carried by the vehicle sense the length of the
motor-to-rail gap and any acceleration of the vehicle causing
changes in the gap. A non-linear feedback circuit responds to the
sensor signals and controls the voltage applied to the phased
windings of the motor to maintain the selected gap. The feedback
circuit provides uniform stability and dynamic response over a wide
range of gap, maintains the selected gap substantially constant
notwithstanding track irregularities and variations in vehicle
loading, and gradually corrects for unevenness. The inertial sensor
is made to be sensitive to vertical acceleration of the vehicle and
insensitive to irregularities of the rail thereby assuring a
"smooth" or "easy" ride notwithstanding irregularities of the rail.
The frequency of the applied voltage is varied upwards from zero to
adjust the linear speed of the motor, and the voltage is increased
with the frequency to compensate for the increase in inductive
reactance of the windings. A wide dynamic range of motor control
voltage is provided to cover the propulsion range from standstill
to high speed without requiring a wide dynamic range in the
feedback control elements.
Inventors: |
Ross; James A. (La Jolla,
CA) |
Assignee: |
Rohr Industries Inc. (Chula
Vista, CA)
|
Family
ID: |
26829077 |
Appl.
No.: |
05/219,713 |
Filed: |
January 21, 1972 |
Related U.S. Patent Documents
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Application
Number |
Filing Date |
Patent Number |
Issue Date |
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131041 |
Apr 16, 1971 |
3638093 |
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Current U.S.
Class: |
104/282; 104/284;
104/293; 318/587; 318/687; 104/290; 318/135; 318/649 |
Current CPC
Class: |
B60V
3/04 (20130101); B60L 13/06 (20130101); B60L
15/005 (20130101); G05D 3/1427 (20130101); B61F
5/383 (20130101); B60L 13/10 (20130101); H02K
41/03 (20130101); Y02T 10/64 (20130101); B60L
2200/26 (20130101); Y02T 10/645 (20130101) |
Current International
Class: |
B60L
13/04 (20060101); B60L 13/10 (20060101); B60L
15/00 (20060101); B60L 13/06 (20060101); B60L
13/00 (20060101); B60V 3/04 (20060101); B61F
5/38 (20060101); B60V 3/00 (20060101); B61F
5/00 (20060101); H02K 41/03 (20060101); G05D
3/14 (20060101); H02k 041/02 () |
Field of
Search: |
;318/687,135,648,649,584,585,586,676,587
;104/89,91,93,148R,148LM,148MS |
References Cited
[Referenced By]
U.S. Patent Documents
Foreign Patent Documents
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1,035,764 |
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Jul 1966 |
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GB |
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1,537,842 |
|
Jul 1967 |
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FR |
|
643,316 |
|
Apr 1937 |
|
DD |
|
707,032 |
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Jun 1941 |
|
DD |
|
Primary Examiner: Miller; J. D.
Assistant Examiner: Huberfeld; H.
Parent Case Text
CROSS-REFERENCE TO RELATED APPLICATIONS
This application is a continuation-in-part of the U.S. Pat.
application of James A. Ross for "Magnetic Suspension and
Propulsion System," Ser. No. 131,041, filed Apr. 16, 1971, now U.S.
Pat. No. 3,638,093, hereinafter sometimes referred to as the
"parent application."
Claims
What is claimed as new and useful and desired to be secured by U.
S. Letters Patent is:
1. The non-linear feedback method of linearizing the voltage vs.
force function of an electroresponsive force field generator whose
generated attractive force with respect to a nonmovable co-acting
member separated therefrom varies directly as the square of the
generator current and inversely as the square of the separation
distance, said method comprising the steps of:
sensing the gap defining the separation distance and any
acceleration of the generator associated with any change in the gap
to produce signals indicative of the length of the gap and the rate
of change of the gap;
deriving from said signals a force proportional feedback voltage
corresponding to a gap stabilizing attractive force to be generated
by the generator which is sufficient against an opposing force
thereon to restore and maintain the generator in a position of
stable equilibrium at a predetermined gap;
deriving from said feedback voltage and said signals non-reactive
and reactive feedback voltage components respectively proportional
to the length of the gap and the frequency of the signals; and
applying to the generator a terminal voltage proportional to the
sum of said non-reactive and reactive voltage components, whereby
said stabilizing attractive force is produced by the generator.
2. The feedback method as in claim 1 wherein the generator is
suspended below its co-acting member and the opposing force is the
weight of the generator due to the acceleration of gravity.
3. The feedback method as in claim 1 wherein the opposing force is
an inertial force acting on the generator.
4. The feedback method as in claim 2 wherein the opposing force has
both gravitational and inertial components.
5. The feedback method as in claim 1 wherein the opposing force is
zero in the absence of an inertial force acting on the
generator.
6. The feedback method as in claim 1 wherein the opposing force is
produced by an equivalent force field generator.
7. The feedback method as in claim 6 wherein the equivalent
generators are physically connected together.
8. The feedback method as in claim 7 wherein the opposing forces of
the equivalent generators are equal at a predetermined value in
which the gaps between the generators and their respective
co-acting members are equal.
9. The feedback method as in claim 7 wherein the opposing forces of
the equivalent generators are zero when the gaps between the
generators and their respective co-acting members are equal.
10. The feedback method as in claim 4 and comprising the further
steps of:
sensing any lateral inertial force acting on the generator in a
direction transversely to the direction of gravity acting thereon
and indicative of a condition creating a need for adjustment of
said predetermined gap, thereby to produce signals indicative of
said lateral inertial force; and
adding said last named signals to said length of gap and rate of
gap change signals to adjust the strength of said force
proportional feedback voltage whereby said predetermined gap is
adjusted sufficiently to satisfy said need.
11. The feedback method as in claim 1 wherein said step of deriving
said non-reactive and reactive voltage components includes the step
of electrically extracting the square root of said force
proportional voltage.
12. The feedback method as in claim 1 wherein said step of deriving
said non-reactive and reactive voltage components includes the
steps of electrically extracting the square root of said force
proportional voltage, electrically multiplying the square root
voltage by the length of gap signal voltage, and differentiating
the square root voltage.
13. The feedback method as in claim 1 wherein said step of deriving
said terminal voltage includes the step of summing said
non-reactive and reactive voltage components.
14. The feedback method as in claim 1 wherein the derivation of the
force proportional and terminal voltages involves multiplications
and summations expressed by the voltage vs. force function
equation:
E = K.sub.3 (.sqroot. F lR = j .sqroot.F K.sub.4 .omega.)
where:
E is the terminal voltage
.sqroot.F lR is the non-reactive voltage component
j .sqroot.F K.sub.4 .omega. is the reactive voltage component
K.sub.3, K.sub.4 are constants
j is the reaction symbol
F is the attractive force; the force proportional voltage
l is the gap length
R is the generator resistance
.omega. is 2.pi.f
f is the sensed signal frequency.
15. The feedback method as in claim 1 wherein the generator is an
electromagnetic device and its generated force field is a magnetic
field.
16. The non-linear feedback method of linearizing the voltage vs.
force function of a polyphase linear electric motor whose generated
magnetic attractive force with respect to a ferromagnetic reaction
rail from which it is suspended and physically separated varies
directly as the square of the motor current and inversely as the
square of the separation distance, said method comprising the steps
of:
sensing the gap defining the separation distance and any
acceleration of the motor associated with any change in the gap to
produce signals indicative of the length of the gap and the rate of
change of the gap;
deriving from said signals a force proportional feedback voltage
corresponding to a gap stabilizing attractive force to be produced
by the motor which is sufficient against an opposing force acting
on the motor to restore and maintain the same in a position of
stable equilibrium at a predetermined gap;
operating a constant amplitude variable frequency polyphase control
voltage;
deriving from said force proportional voltage, from said signals
and from said polyphase voltage per phase thereof non-reactive and
reactive feedback voltage components respectively proportional to
the length of the gap and the frequency of the polyphase voltage;
and
applying to the motor a polyphase terminal voltage which is
proportional for each phase thereof to the sum of said non-reactive
and reactive voltage components, thereby to produce said
stabilizing attractive force at any frequency upwards from zero of
said polyphase control voltage.
17. The feedback method as in claim 16 wherein the magnetic field
of the motor suspends and propels the same along the rail and
wherein the motor linear speed along the rail is a function of the
frequency of the magnetic field alternations.
18. The feedback method as in claim 17 wherein the reactive voltage
component for each phase is proportional to the first derivative of
the product of said constant amplitude variable frequency,
polyphase control voltage and the square root of said force
proportional voltage, and the nonreactive voltage component for
each phase is proportional to the product of the gap length times
the square root of the force proportional voltage times said
polyphase control voltage.
19. The feedback method as in claim 18 wherein the products and
summations are expressed by the voltage vs. force function
equation:
E = K.sub.1 (.sqroot.F.sub.M lR + j .sqroot.F.sub.M K.sub.2 f)
where:
E is the polyphase alternating current terminal voltage
.sqroot.F.sub.M lR is the nonreactive voltage component
j.sqroot.F.sub.M K.sub.2 f is the reactive voltage component
F.sub.M is the attractive force between the motor and the rail; the
force proportion voltage
l is the gap length
R is the motor winding resistance
f is the frequency of the terminal voltage
K.sub.1, K.sub.2 are constants.
20. The method of combined suspension and propulsion of an electric
linear motor support for a high speed tracked transport vehicle
which comprises the steps of
disposing an electric linear motor below a magnetic rail support
therefor,
controlling the voltage and current relationship of the motor to
establish an attractive magnetic field between the motor and rail
sufficient to suspend the mass including the motor and its load
against the force of gravity and at a selected gap defining the
displacement of the motor from the rail,
sensing the gap displacement and any acceleration of said mass
associated with any change in the gap displacement,
adjusting said voltage and current relationship of the motor in
response to signals sensed by the displacement and acceleration
sensors to maintain said selected gap displacement,
adjusting said voltage and current relationship to produce
alternations of the suspension field and to move the same along the
motor and in linear thrust producing relation to the rail to move
the mass along the rail at a speed determined by the frequency of
said field alternations,
varying the frequency of said field alternations to adjust the
linear speed of the mass, and
adjusting said voltage and current relationship as a function of
frequency to compensate for increasing motor impedance with
frequency thereby to maintain the strength of the suspension field
constant at all propulsion speeds.
21. A feedback control system comprising:
a fixed member;
an electroresponsive force field generator separated in free space
at a predetermined separation distance from said fixed member for
generating a force field therewith and resultant attractive force
therebetween wherein the attractive force varies as the square of
the generator current and inversely as the square of the separation
distance;
means carried by the generator for producing a force proportional
voltage proportional to the attractive force which is required to
be generated by the generator to restore and maintain the same in
stable equilibrium at said predetermined separation distance
against an opposing force acting on the generator; and
means responsive to said force proportional voltage for producing
and applying to said generator a terminal voltage sufficient to
enable the same to generate said required attractive force.
22. A feedback system as in claim 21 wherein said terminal voltage
producing means includes:
square rooter means for electrically producing a square root
voltage which is the square root of said force proportional
voltage.
23. A feedback control system as in claim 21 wherein:
said force proportional voltage means includes sensing means for
producing a signal proportional to the separation distance; and
said terminal voltage producing means includes:
square rooter means for electrically producing a square root
voltage which is the square root of said force proportional
voltage; and
multiplier means for electrically producing a voltage which is the
product of said square root voltage and said distance proportional
signal.
24. A feedback control system as in claim 23 wherein:
said square root voltage has a frequency proportional to any
variations in said distance proportional signal; and
said terminal voltage producing means also includes:
means for differentiating said square root voltage to produce a
voltage proportional to its frequency; and
means for electrically summing said product voltage and said
frequency proportional voltage.
25. A feedback control system as in claim 24 wherein said terminal
voltage is produced in accordance with the equation:
E = K.sub.1 F (Rl = jK.sub.2 f)
where:
E is the terminal voltage
F is the required attractive force
R is the generator resistance
l is the separation distance
f is the frequency of the square root voltage
K.sub.1 and K.sub.2 are constants.
26. A suspension apparatus having a force generator, a co-acting
support therefor, a feedback circuit for controlling a suspension
force produced by said force generator to suspend the same in free
space from said support therefor without contact therewith and
against the force of gravity acting thereon to thereby maintain the
generator in a state of stable equilibrium at a selected gap length
within a range of selectable gap lengths between said generator and
support, said feedback circuit having at least one input selected
from a group of inputs which respectively represent the position,
velocity and acceleration of the generator associated with any
change in the gap, an output signal applicable to said force
generator to control said suspension force, and circuit means
responsive to said inputs to produce said output signal.
27. An apparatus according to claim 26, wherein said feedback
circuit includes means for setting the magnitude of the suspension
force sufficient to counterbalance the force of gravity at a
preselected nominal gap within said range of gaps.
28. An apparatus according to claim 26 wherein the magnitude of the
suspension force is regulated by sensing the vertical position of
the generator and the acceleration of change of that position.
29. An apparatus according to claim 26, wherein said circuit means
includes an element having an output proportional to a mathematical
root of the input thereto.
30. An apparatus according to claim 26, wherein said circuit means
includes an element having an output proportional to a mathematical
differential of the input thereto.
31. A feedback circuit for controlling the voltage of an
electroresponsive force field generator which is attracted by its
force field toward a co-acting member and held physically separated
therefrom by an opposing force thereon wherein the generator is
maintained at a preselected separation distance when the attractive
and opposing forces are equal and wherein the attractive force
varies inversely as the square of the separation distance and
directly as the square of the generator current, said feedback
circuit comprising a first input having X signals which vary with
the displacement distance and a second input having signals which
vary with any acceleration of the generator associated with any
change in the separation distance, and output having a feedback
voltage for controlling the generator voltage to maintain the
attractive force equal to the opposing force, and means responsive
to the signals of said first and second inputs for producing said
feedback voltage.
32. A suspension-propulsion feedback system comprising:
a ferromagnetic support rail having linear thrust producing
reaction means;
an electric linear motor disposed beneath said rail in spaced
relation therewith defining an air gap therebetween, said motor
having plural phase windings for producing a combined motor
suspension and propulsion magnetic field with respect to said rail
and its reaction means;
a controllable plural phase power amplifier source of variable
amplitude and variable frequency voltage for respectively
energizing said plural phase windings; and
gap length and frequency control means carried by said motor for
simultaneously regulating the amplitude of each phase of said
energizing voltage to restore and maintain the motor in stable
equilibrium at a predetermined gap and for simultaneously
regulating the frequency of each phase of said energizing voltage
to set the linear speed of the motor along the rail.
33. A feedback system as in claim 32 wherein said gap length
control means includes:
means for sensing the gap length and any acceleration of the motor
associated with any change in the gap length.
34. A feedback system as in claim 33 wherein said gap length
control means also includes:
means responsive to signals produced by said sensing means for
producing a feedback voltage input to said power amplifier source
to regulate the amplitude of its output voltage.
35. A feedback system as in claim 34 wherein said signal responsive
means includes:
operational amplifier means responsive to said signals for
producing a force proportional voltage which is proportional to the
magnetic motor-to-rail attractive force required to maintain the
motor at said predetermined gap against the force of gravity acting
thereon; and
means for electrically extracting the square root of said force
proportional voltage to produce a square root voltage.
36. A feedback system as in claim 35 wherein:
said frequency control means comprises a plural phase source of
constant amplitude and variable frequency control;
first multiplier means for electrically producing per phase of said
control voltage an output which is the product of the control
voltage amplitude times said square root voltage;
second multiplier means for electrically producing per phase of
said control voltage the product of said first multiplier means
output times the length of gap signal to produce a gap compensated
control voltage component;
means for differentiating per phase of said control voltage the
product output of said first multiplier means to produce a
frequency compensated control voltage component; and
means per phase of said control voltage for electrically summing
said gap and frequency compensated voltage components.
37. A feedback system as in claim 36 including means for
simultaneously varying the frequency per phase of said control
voltage.
Description
BACKGROUND OF THE INVENTION
Heretofore others have suggested linear motors utilizing the same
magnetic flux for suspension and propulsion of tracked vehicles.
United States Pat. No. 782,312 (1905) to Alfred Zehden and French
Pat. No. 1,537,842 (1968) to Jeumont-Schneider Electromechanical
Construction Company, for example, teach combined propulsion and
suspension of a linear induction motor by magnetic attraction of
the motor upwardly toward its support rail which also serves as the
reaction rail. Zehden discloses triphase windings, and the French
patent teaches changes in power frequency to effect changes in
propulsion speed. The French patent further teaches the use of gap
sensing operative in an electronic feedback circuit for maintaining
suspension of the motor below its support rail at a controlled air
gap therebetween, thereby to avoid physical contact with the rail
both at standstill and during propulsion along the rail. Zehden
employs a rail engaging wheel support and does not disclose a
feedback control circuit.
German Pat. Nos. 643,316 (1937), 44,302 (1938), and 707,032 (1941)
to Hermann Kemper disclose the suspension of tracked vehicles by
use of electromagnets disposed below a support rail and
magnetically attracted thereto while maintaining a controlled air
gap therebetween, thus avoiding physical contact of the
electromagnets with the rail.
The 1941 Kemper patent and the French patent disclose similar
arrangements utilizing magnetic attraction for guidance and
switching of the magnetically suspended vehicle.
The 1937 Kemper patent suggests that the electromagnets used for
suspension can be configured for polyphase operation for propulsion
of the vehicle along the track, operating for this purpose in the
manner of polyphase induction motors. Recent developments of German
industry in the transportation field, however, while apparently
following the teachings of Kemper with respect to achieving
magnetic suspension, tend to follow Kemper's suggested alternative
propulsion arrangement of using separate electromagnets operative
with their own reaction rail in a conventional polyphased linear
induction motor mode.
The suspension arrangement of the 1938 Kemper patent (Addition to
the 1937 patent), in common with the teaching of the 1937 patent,
senses motor position with respect to the rail (gap), but further
senses rate of change of that position (motor velocity), and change
in motor energy state (motor suspension current) to provide a motor
control voltage which is operative over a wide range of gap X
(twice normal gap a). The motor voltage may be d.c. or a.c. and is
characterized as being positive or negative over-voltages for
achieving arbitrarily high acceleration of the energy level
contained in the motor windings.
The 1938 Kemper patent is concerned with providing feedback for
preventing oscillations of the suspended vehicle caused by the
kinetic energy acquired by the vehicle in response to a correction
of position and, further, in preventing high acceleration of change
of motor energy level from causing further changes in energy level
when the correct level is reached. The position feedback voltage
e.sub.x produces a directing magnetic force to return the suspended
vehicle to the correct location relative to the rails, and the
damping or velocity feedback voltage e.sub.d assures that the
correcting movement can be made to a more or less damped
oscillation. A report feedback potential e.sub.r is made to be
proportional to the motor current and, in turn, provides a measure
of the momentary energy state of the motor magnet. The sum of the
position feedback voltage e.sub.x and the damping voltage e.sub.d
constitutes a command voltage e.sub.b which starts the energy
addition or reduction when a change in gap is sensed. The report
potential e.sub.r opposes the command potential e.sub.b to prevent
further changes in the energy state as soon as the correct level is
reached.
The feedback provided by the Kemper Addition Patent is made to
produce a smooth ride of the suspended vehicle by designing a pull
force curve (curve III of FIG. 4) wherein position feedback voltage
e.sub.x is caused to fall off for increasing gap distance, the
directional pull force being sufficient, however, to return the
vehicle to the correct location but being limited to a desirable
maximum value which results in limiting the tracking of the vehicle
in relation to the rail track when moving rapidly. Additional
absorption of rail nonuniformities is achieved by avoiding
excessive suppression of the electrical inertia characteristics of
the feedback regulator circuits, the smooth ride resulting because
the feedback is not required to force distance corrections for
deviations which exist only in short sections of the rail track
whereby the vehicle is caused to follow only the average from a
number of different regulation impulses.
Automotive News for October 1970 describes an active
spring-hydraulic suspension system for an air cushion supported
tracked vehicle which employs vertical and lateral acceleration
sensor inputs to a computer which calculates the forces necessary
to maintain the vehicle body on a smooth path and with banking on
turns.
In the aforesaid copending parent application, Ser. No. 131,041, of
James A. Ross there is disclosed a tracked vehicular transportation
system employing polyphased linear motors both for suspension and
propulsion in which each motor is magnetically attracted upwardly
by its magnetic field toward a support rail with a controlled air
gap maintained therebetween, and its suspension magnetic field is
also used to translate the motor and its supported vehicle along
the track at a speed related to the frequency of the polyphase
alternating current applied to the motor.
Although any number of phases could be used, a three phase design
is disclosed because it is the simplest motor construction having
the desirable characteristic of providing nearly constant pole
attraction as a function of phase rotation. The propulsion system
is a variable reluctance, synchronous speed type wherein the rail
is provided with repetitive magnetic discontinuities (notches), or
alternatively, the propulsion system is a linear induction motor
type wherein the rail is provided with either a continuous
conductive reaction strip or a squirrel cage winding (shorted
rotor). Other disclosed propulsion systems are of the wound rotor
and hysteresis types.
The terminal voltage applied to the polyphased motor windings to
produce the attractive suspension force as well as the moving field
for propulsion is controlled by a non linear-feedback circuit which
uses signals from displacement and inertial sensors carried on the
vehicle for maintaining a selected air gap. The feedback is non
linear in order to compensate for the nonlinearity of the motor
characteristic as a function of gap length and of feedback
operating frequency. The attractive force produced by the magnetic
field of the motor is proportional to the square of the motor
current and inversely proportional to the square of the gap length.
The motor impedance, moreover, is resistive at zero frequency and
largely inductive at frequencies such as 10 to 30 hertz which are
relatively high for the feedback apparatus.
The circuit elements of the feedback circuit provide the motor
terminal voltage in accordance with the following equation which
expresses the relationship between the motor terminal voltage and
the resulting attractive magnetic force produced between the motor
and its support rail:
E = K.sub.3 .sqroot.F (lr + jK.sub.4 .omega.) where
.omega. = 2.pi.f
E = terminal voltage
l = air gap length
f = frequency in hertz (cycles/second)
K.sub.1, K.sub.2 = constants
F = attractive magnetic force
j = reaction symbol.
In order to provide stable suspension of the vehicle, whether at
standstill or some propulsive speed, and at a selective gap which
may range from substantially zero to one-half inches, the motor
terminal voltage E, whether d.c. at standstill or a.c. at the
propulsive speed, produces an attractive magnetic force F which is
opposite to the gravitational and inertial forces acting on the
vehicle and sufficient to restore and maintain the same in stable
suspension. The feedback circuit responds to signals from the
displacement and inertial sensors to produce various voltages
indicative of these gravitational and inertial forces. For example,
in a specific circuit arrangement, a voltage input of -4 volts to
the square rooter element of the circuit indicates a gravitational
force of 1 g which, of course, is the weight of the vehicle
including its support motors. When this is the only force on the
vehicle, the magnetic attractive force F produced by the motor
terminal voltage E is just sufficient to support the vehicle
against gravity at the selected gap.
Signals from the displacement and inertial sensors pass in parallel
paths through displacement and accelerometer channels in the input
portion of the feedback circuit. The displacement channel produces
displacement signals indicative of the length of the gap, velocity
signals which are derived from differentiated displacement and are
indicative of the rate of change of displacement, and change in
loading signals which are derived from integrated displacement. The
velocity signals range in frequency from 1.2 to 5 hertz. The change
in loading signals range in frequency from d.c. to 1.2 hertz. The
range of frequencies of maximum interest in the displacement
channel thus extends from d.c. to 5 hertz.
Signals from the displacement channel are algebraically summed with
signals from the accelerometer channel which has a frequency range
of maximum interest extending from 0.3 to 30 hertz. Partial
integration of the accelerometer feedback signal provides a
quasi-velocity feedback which is effective from a frequency of the
order of 10 hertz down to 4 hertz below which the differentiated
displacement signal provides the velocity feedback.
The square rooter element of the feedback circuit takes the square
root of the combined displacement and accelerometer channel signals
to produce a voltage corresponding to the equation quantity
.sqroot.F which is thereafter multiplied by the displacement
function (lR) and the frequency function (jK.sub.4 .omega.),
respectively, these equation functions being performed by
mutliplier and amplifier-differentiator circuit elements. These
circuit elements respectively provide d.c. and a.c. paths for their
inputs, the d.c. path providing a voltage which increases with the
gap and the a.c. path providing a voltage which increases with
increasing feedback frequency, as is required to linearize the
motor response with frequency. The a.c. path includes a perfect
differentiator which provides a first derivative of the input over
a frequency range of from essentially zero to 200 hertz.
The combined outputs of the multiplier and amplifier-differentiator
elements produce a unidirectional feedback voltage which represents
the equation quantity .sqroot.F (lR + jK.sub.4 .omega.). The
combined circuit gain required to produce suspension against
gravity accounts for the constant K.sub.3 in the equation.
The varying frequency voltage required for propulsion at speeds
upward from zero is provided by a constant amplitude variable
frequency three phase oscillator, the amplitude of each phase of
which is increased as a function of the frequency by an imperfect
differentiator for each phase to compensate for the increase in
motor impedance due to the increase in inductive reactance with
frequency. The differentiation is imperfect to assure an output at
zero frequency and thus provide the magnetic flux required in the
motor-to-rail gap to establish suspension when the system is in
operation at standstill.
The unidirectional variations of the feedback voltage are made
essentially to modulate the imperfect differentiator outputs for
each phase, it being a first input to each of three multipliers for
the three phases, the other input for each of the multipliers being
one of the differentiator outputs. Each of the multiplier outputs
gives the product of the feedback voltage and the instantaneous
value of each of the phased voltages in accordance with the
three-phase variation thereof.
The output from each multiplier for each phase passes into a
controllable power supply having three outputs, one for each of the
phased windings of the motor, the voltage output of each being
controlled according to the variation of three phase electrical
energy with time, including the special case of zero frequency
wherein the phased outputs constitute "frozen" instantaneous values
which do not vary with time until a frequency variation is again
produced to provide propulsion. Highly efficient controllable
amplifiers of high power capabilities such as the Class D type or
the gated-silicon-controlled-rectifier type are employed to provide
propulsive power for passenger-carrying railroad car type vehicles
weighing thousands of pounds.
An inertial or accelerometer type sensor which senses any
acceleration in the vertical direction of the motor and its
supported mass as the same moves up and down in space is preferred
since it provides signals indicative of such movements without
regard to the motor-rail spacial relationship. Thus, the
accelerometer sensor is not sensitive to irregularities in the
track and does not pass them on to the passengers in the form of
vibrations or jolts. On the other hand, the gain of the
displacement channel is reduced as a function of gap change
frequency and only a mean gap is maintained by the displacement
sensor. An alternative acceleration feedback sensor which senses
relative acceleration of the suspended mass with respect to the
rail is suggested for use as a substitute for the
inertial-reference accelerometer in the feedback circuit when it is
desired that the vehicle closely follow the rail for technical
reasons or to avoid the higher costs of the inertial accelerometer.
Hall-effect transducers which sense the flux in the air gap are
suggested as a suitable sensor for such purpose.
The feedback loop that includes the inertial sensor makes a second
order correction to the overall feedback network of the order of
10db of feedback over the frequency of interest which is from 0.5
to 5 hertz. This makes the system insensitive to second order
variations such as changes in coil resistance with temperature and
variations in the d.c. gain and a.c. gain of the feedback network
which may change from day to day with weather changes, and for
other reasons.
As aforementioned, the force exerted magnetically by the motor to
provide suspension varies as the square of the motor current and
inversely as the square of the gap length. This is a non-linear
relation. However, the d.c. flux in the air gap remains the same
for different gap lengths when the current to gap ratio remains
constant as it does, for example, when the current is doubled when
the gap is doubled, the magnetizing force or ampere turns per unit
length of gap remaining the same. Non-linear elements in the
feedback circuit, such as the square-rooter circuit, linearize the
voltage vs. force function for all gap lengths and thus allows the
dynamic response of the feedback signals to be constant and
provides constant stability for the system. The resultant
linearization of the feedback circuit also provides constant gain
at all operating frequencies of the polyphase power and
corresponding propulsive speeds. This assures a smooth ride at all
vehicle speeds. The smoothness of the ride, moreover, can be
adjusted by adjustment of the feedback circuit, it being
unnecessary to change the motor or any related parts of the
structure.
The feedback circuit assures the stability of the vehicle with
respect to the track, compensates for varying passenger loading and
thrust due to wind, and gradually corrects for unevenness of the
track. The feedback circuit also inherently maintains lateral
stability and any lateral perturbation is restored in a damped
manner without overshoot.
SUMMARY OF THE INVENTION
The present invention relates generally to the transportation field
and more particularly to a high speed tracked transport vehicle
which uses the same linear electric motors for both suspension and
propulsion, such as disclosed in the aforesaid copending parent
application of James A. Ross, and which additionally may use such
motors for vehicle guidance and banking.
The present invention follows the basic principles and incorporates
the fundamental features of the parent application while providing
improvements in the composition and functioning of the non-linear
feedback circuit which controls both the magnitude and frequency of
the motor terminal voltage to achieve suspension and propulsion at
selected propulsion speeds, or suspension alone at standstill.
Specifically, the feedback control circuit of the present
invention, while employing circuit elements for performing the
multiplications and summations of the voltage vs. force function
equation:
E = K.sub.3 .sqroot.F (Rl + jK.sub.4 .omega.)
as in the parent application, expresses this equation in the
form
E = K.sub.1 .sqroot.F (lR + jK.sub.2 f)
where:
F is the attractive magnetic force
E is the terminal voltage
l is the air gap length
R is the winding resistance
f is the propulsion frequency in hertz
K.sub.1, K.sub.2 are constants
j is the reaction symbol.
The square root function .sqroot.F is developed from the sensor
signal paths, as in the parent application. The multiplication of
this function times displacement and propulsion frequency, however,
are performed in the propulsion frequency control channel.
A first multiplier produces the product of the .sqroot.F function
times each phase of a constant applitude three phase voltage of
selected frequency which may be zero at standstill or a specific
frequency corresponding to a desired propulsion speed. This product
which represents K.sub.1 .sqroot.F in the equation is the input to
a second multiplier operating in parallel with a perfect
differentiator. The second multiplier produces the product K.sub.1
.sqroot.F lR and the differentiator produces the product K.sub.1
.sqroot.F K.sub.2 f, and these products are summed and provided as
the input to the three phase controllable power amplifiers which
supply the terminal voltages to the three phase motor windings.
This improved feedback circuit arrangement eliminates the imperfect
differentiator of the parent application which increased the
amplitude of the oscillator signal, of each phase as the oscillator
frequency increased. This required that the following multipliers
be operated over an extremely wide dynamic range. A perfect
differentiator which in the circuit arrangement of the instant case
provides the voltage vs. frequency function, follows the
multipliers and thus permits the motor terminal voltage to be
increased with frequency for any desired propulsion speed without
exceeding the dynamic operating range of the multipliers.
The non-linear feedback circuit disclosed and claimed in the parent
application is a species of the generic invention herein disclosed
and claimed wherein an electroresponsive force field generator and
a coacting member separated or spaced therefrom are attracted
toward each other by the force field set up between them and are
held separated from each other at a selected gap by an opposing
force, it being the function of the non-linear feedback circuit to
so adjust the voltage of the electroresponsive force field
generator that the force produced by it is at all times sufficient
relative to the opposing force to restore and maintain stable
equilibrium at the selected gap.
In the species of the invention disclosed and claimed in the parent
application, the magnetic force field and feedback circuit
arrangements are made to be responsive to opposing force
relationships wherein the opposing force is gravity and other
acceleration forces tending to upset the stable equilibrium of the
suspended vehicle and its support motors.
In the present invention, force field and feedback circuit
arrangements embodying the generic invention are also made to be
responsive to laterally directed displacement and acceleration
forces on the vehicle such as may be caused by wind loads or may
occur during turning movements, to thus accomplish controlled
magnetic guidance and banking of the vehicle.
The foregoing and other features of the invention will become more
fully apparent from the following detailed description with
reference to the accompanying drawings.
BRIEF DESCRIPTION OF THE DRAWINGS
FIG. 1 is a schematic view of a force field generator embodying the
voltage vs. force functions employed in the present invention;
FIG. 2 is a schematic view of a tracked vehicle and its support
motors for achieving magnetic suspension and banking in accordance
with the feedback principles of the present invention;
FIG. 3 is a schematic view of a tracked vehicle and its linear
motors for achieving suspension and guidance of the vehicle;
FIG. 4 is a block diagram of a feedback control circuit for
supplying the motor terminal voltages E.sub.1 and E.sub.2 of FIG.
2;
FIG. 4A is a schematic circuit diagram of one embodiment of the
block diagram of FIG. 4;
FIG. 5 is a complete block diagram of the electrical system for
achieving suspension and propulsion of a tracked vehicle and its
linear electric support motors;
FIGS. 6A and 6B, taken together, constitute a schematic circuit
diagram of one embodiment of the block diagram of FIG. 5;
FIGS. 7A and 7B are graphs showing speed vs. frequency
relationships for synchronous relucatance and inductance motors
respectively;
FIG. 8 is a plot of the open loop response of the system of FIGS.
6A and 6B to a disturbing force; and
FIGS. 9 and 10 are graphs showing curves which represent the
characteristic response of the system to load and track
disturbances.
DETAILED DESCRIPTION
Referring to FIG. 1, an electroresponsive force generator M and a
member R are separated physically by the air gap distance or length
l. Generator M and member R are mutually attracted toward each
other as indicated by the force field f set up therebetween by
generator M when a voltage E supplies a I thereto, the attractive
force being designated F.sub.M . Assuming the member R to be fixed,
that is, nonmovable, the force F.sub.M is directed to depict that
the generator M is attracted toward member R.
When the generator M, for example, is an electromagnet, or an
electric linear motor, and the member R, for example, is a
ferromagnetic rail, the force F.sub.M varies as the square of the
current flowing in the winding of the electromagnetic device M and
inversely as the square of the air gap length l between the device
M and the rail R in accordance with the equation:
F.sub.M = K.sub.1 (I.sup.2 /l.sup. 2) (1)
where:
K.sub.1 = [ A/(8 .times. 981)] (4.pi.N/10).sup.2 (1.sub.1)
where:
A is the area of attraction in square centimeters
N is the number of turns in the winding of electromagnetic device
M
Equation (1) is derived from two basic equations expressing
magnetic circuit principles, one being that the magnetic force
F.sub.M between two parts of a magnetic circuit varies as the
product of their area of attraction A and the square of the
magnetic flux density B at their interface:
F.sub.M = AB.sup.2 /(8.pi. .times. 981) (1.sub.2)
where:
B is the flux density in gauss
F.sub.M is the force in grams
and the second principle being that the magnetizing force H
required to set up a flux in an air gap l between the parts is
equal to the flux density B:
B = H = 4 .pi. NI/10l (1.sub.3)
where:
NI/l is ampere turns per centimeter
l is air gap length in centimeters
B is flux density in gauss
Combining equations (1.sub.2) and (1.sub.3):
F.sub.M = [ A/(8.pi. .times. 981)] (4.pi.NI/10l ).sup.2
= [A/(8.pi. .times. 981)] (4.pi. N/10).sup.2 (I/l).sup.2
= K.sub.1 (I/l).sup.2 = K.sub.1 (I.sup.2 /l.sup.2) (1)
It will be noted that the magnetic force F.sub.M is the same for
any air gap within a wide range of air gaps as long as the ampere
turns per unit length or the air gap, namely, the ratio NI/l, is
constant. Thus, for example, the attractive force will remain the
same if the current is doubled when the gap length is doubled.
The linear relationship between the current and gap length is
apparent from a re-write of equation (1):
I =(.sqroot.F.sub.M l)/.sqroot.K.sub.1 (1.sub.4)
where the current varies directly with the air gap and as the
square root of the force F.sub.M. The current varies directly as
the voltage E across the winding of the electromagnetic device M
and can be changed by changing the voltage:
I = E/(R + j.omega. L) (2)
where:
R + j.omega.L is the winding impedance
R is the winding resistance
L is the winding inductance
j is the reactive symbol
.omega. is 2.pi.f
f is frequency in hertz (cps)
E is the voltage across the impedance.
Combining equations (1.sub.4) and (2):
E= [(.sqroot.F.sub.M l/.sqroot. K.sub.1) ] (R + j.omega.L)
(2.sub.1)
the inductance of an electromagnetic device M separated from a
ferromagnetic member R in a magnetic circuit the therewith having
an air gap 1 therebetween varies inversely as the length of the air
gap:
L = K.sub.2 /l (3)
Combining equations (2.sub.1) and (3):
E = K.sub.3 .sqroot.F.sub.M (lR + K.sub.4 j.omega.) (4)
or
E = K.sub.3 .sqroot.F.sub.M lR + K.sub.3 .sqroot.F.sub.M K.sub.4
j.omega. (4.sub.1)
In order to keep equation (4.sub.1) in balance, any changes in
F.sub.M and/or in l in magnitude and rate must be accompanied by a
change in E, and any such changes in E must be both in magnitude
and rate of change, the latter giving rise to a frequency component
in E, and this, in turn, causing the reactive voltage component
K.sub.3 .sqroot.F.sub.M K.sub.4 j.omega. to increase directly in
proportion to the increase in the frequency. The voltage E, of
course, must increase, as required, to compensate for the increase
in the winding impedance due to the increase in inductive reactance
with frequency. At zero, or very low frequencies, the winding
impedance is substantially resistive, and the voltage E is
substantially equal to the resistive voltage component
K.sub.3.sqroot.F.sub.M lR, the voltage E in such case being
characterized only by its magnitude, being essentially d.c.
Referring again to FIG. 1; assume that an opposing force F.sub.O is
acting on the force generator M in a direction opposite to the
attractive force F.sub.M. If the attractive force F.sub.M is made
to equal the opposing force F.sub.O, the separation distance l will
be constant and the generator mass M will be in a state of stable
equilibrium.
In the aforesaid parent application Ser. No. 131,041, a tracked,
high speed vehicle is disclosed having four linear electric motors
mounted at the four corners thereof for suspension and propulsion
of the vehicle from and along the track by magnetic attraction.
This arrangement is disclosed, in part, in FIG. 2, wherein the rear
motors M.sub.1 and M.sub.2 are shown in spaced dependent relation
to their respective support rails R.sub.1 and R.sub.2 , being
separated therefrom by the air gaps l.sub.1 and l.sub.2. The rails
are supported in fixed relation on the track generally designated
T.
The vehicle V which moves along the track T is supported by and
secured to the front and rear motors of which the rear motors
M.sub.1 and M.sub.2 are shown secured to the vehicle as by the
mounting brackets schematically designated b.sub.1 and b.sub.2.
The magnetic attractive forces F.sub.M1 and F.sub.M2 respectively
of the motors M.sub.1 and M.sub.2 are opposed by the forces
F.sub.O1 and F.sub.O2. These opposing forces may be considered
generally to be acceleration forces expressed by the equation:
F = Ma (5)
where:
F is the acceleration force
M is the mass of the body acted upon by the force F
a is the acceleration of the body represent W
When the air gaps l.sub.1 and l.sub.2 are static, there being no
change in the gaps, the corresponding forces F.sub.O1 and F.sub.O2
represent the weights supported respectively by the magnetic forces
F.sub.M1 and F.sub.M2 of motors M.sub.1 and M.sub.2. Weight W is
the force which gravitation exerts upon a body and is equal to the
mass of the body times the local acceleration of gravity g,
thus:
F = Ma
as before set forth in equation (5). Now with g substituted for a,
and W substituted for F:
W = Mg
and
M = W/g (6)
Motors M.sub.1 and M.sub.2 by their attractive forces F.sub.M1 and
F.sub.M2 support their own weights W.sub.M1 and W.sub.M2 and one
fourth the weight Wv/4of the vehicle, thus: ##SPC1## 4
Vehicle V carries a pair of position or placement sensors S.sub.P1
and S.sub.P2 which respectively sense the length of the air gaps
l.sub.1 and l.sub. 2 associated with motors M.sub.1 and M.sub.2.
Signals from these sensors operate in their respective feedback
circuits, subsequently to be described, to produce voltages therein
which represent the attractive forces F.sub.M1 and F.sub.M2
required to produce the voltages E.sub.1 and E.sub.2 for support of
the motors M.sub.1 and M.sub.2 at selected gaps l.sub.1 and
l.sub.2, such representative voltages corresponding to the voltage
component F.sub.M of equation (4).
When it is desired to maintain constant motor gaps notwithstanding
changes in passenger loading, or wind loading, on the vehicle, such
changes will, in turn, change the opposing forces and the gaps. The
position sensors, however, sense the gap changes and produces
signals which are integrated to produce appropriate adjustment in
the feedback voltages representing the forces F.sub.M1 and
F.sub.M2. These signals, moreover, are differentiated to provide
velocity feedback for dampening adjustment of these voltages.
Vehicle V further carries accelerometer sensors S.sub.A1 and
S.sub.A2 which are made to sense up and down accelerations of the
vehicle caused, for example, by variations in the vertical radius
of curvature of the track to thus produce signals for the further
adjustment of the feedback voltages representing the magnetic
forces F.sub.M1 and F.sub.M2 and, further, by the integration of
such signals, to develop velocity feedback voltages for the
development of the reactive voltage component of equation (4).
A second pair of accelerometers S.sub.A4 and S.sub.A5 are carried
on the vehicle and directed to sense lateral accelerations occuring
during turning movements of the vehicle so that signals therefrom
may be used to produce relative adjustments of the gaps l.sub.1 and
l.sub.2 for banking purposes, thereby obviating the need for
banking the track and rails R.sub.1 and R.sub.2. Thus, for example,
referring again to FIG. 2, and assuming that the vehicle V is
caused to move in a turn to the left, the sensors S.sub.A4 and
S.sub.A5 will sense acceleration forces directed to the right of
the vehicle, and signals from sensor S.sub.A4 associated with motor
M.sub.1 will cause a decrease in gap l.sub.1 and sensor S.sub.A5
associated with motor M.sub.2 will cause an increase in gap
l.sub.2, thereby to effect the desired banking to negotiate the
left turn.
Referring now to FIG. 3, there is shown thereon a vehicle V.sup.1
having three linear electric motors M.sub.3, M.sub.4 and M.sub.5 of
which M.sub.3 is used for suspension and propulsion, or for
suspension alone, and motors M.sub.4 and M.sub.5 are used for
guidance and propulsion, or for guidance alone. Their respective
force fields are designated f.sub.3, f.sub.4 and f.sub.5, and are
generated in relation to their associated fixed rails R.sub.3,
R.sub.4 and R.sub.5 in the same manner as the force fields f.sub.1
and f.sub. 2 of motors M.sub.1 and M.sub.2 of FIG. 2.
The gaps l.sub.4 and l.sub.5 will normally be equal so that the
magnetic attractive forces F.sub.M4 and F.sub.M5 will also be equal
and, being opposite, will present the required opposing force, each
to the other, to maintain balance. In this case, the attractive
forces, at equal gap lengths l.sub.4, l.sub.5, may be set at any
desired strength upwards from zero. At zero force setting, of
course, there would be no force fields f.sub.4 and f.sub.5.
Considering first the zero force field setting at equal gaps, it
will be presumed that provision is made, as subsequently described,
for producing either of the forces F.sub.M4 and F.sub.M5 as its
associated motor M.sub.4, M.sub.5 is moved with the vehicle to
increase its gap l.sub.4 or l.sub.5 above the equal gap setting In
such case, the generated attractive force will setting. in
proportion to the increase in gap and will oppose the acceleration
force on the vehicle which caused the particular gap l.sub.4 or
l.sub.5 to increase. In this case, one of the accelerometer sensors
S.sub.A4 or S.sub.A5 will aid in the development of the attractive
force required to overcome the lateral acceleration force. When the
acceleration ceases, the other sensor will generate an opposing
attractive force to control the deceleration of the vehicle upon
return of the same to the equal gap condition.
When it is desired to use the force fields f.sub.4 and f.sub.5 for
propulsion, in addition to guidance, some suitable strength of
opposing attractive forces F.sub.M4 and F.sub.M5 is maintained at
all times.
The feedback circuits of FIGS. 4 and 4A are taken from the parent
application and are incorporated in this disclosure as embodiments
of suitable circuitry for developing the magnetic attractive forces
F.sub.M1 to F.sub.M5 of FIGS. 1 to 3, the feedback circuits for
this purpose performing the multiplications and summations of
equation (4). Other disclosures of the parent application are
incorporated herein by reference to that application.
Referring first to FIG. 4, the accelerometer 20 represents any of
the accelerometer sensors S.sub.A1 and S.sub.A2 of FIG. 2 and
S.sub.A3 of FIG. 3 which have a mass of relatively appreciable
magnitude disposed to be sensitive to vertical accelerations. It
also represents either of accelerometer sensors S.sub.A4 and
S.sub.A5 as the same are employed in the FIG. 2 and FIG. 3
arrangements to sense lateral acceleration and thereby provide
inputs to the feedback circuits of motors M.sub.1 and M.sub.2 and
motors M.sub.4 and M.sub.5 respectively, in the same manner as
sensors S.sub.A1 and S.sub.A2 provide inputs to their respective
feedback circuits.
Accelerometer 20 may be of a piezoelectric type, such as Endevco
type 2200, or a servo type such as developed for space use which
does not have the very low frequency "noise" and random variations
characteristic of the piezoelectric types.
Signals from accelerometer 20 pass through a compensating network
21 which alters the frequency vs. amplitude response thereof to
provide about 10 db of feedback within the range of frequencies of
the order of 1/2 to 5 hertz to make the suspension system
insensitive to second order variations such as variations in motor
magnetic structure, variations in the a.c. resistance of windings,
winding resistance variations with temperature, d.c. and a.c. gain
variations in the feedback network, and instability at certain gap
lengths. Network 21 also integrates the accelerometer signals to
provide velocity feedback which is effective over a range of
frequencies of the order of 4 to 10 hertz.
Position transducer 22 is a sensor element which provides length of
gap information and represents any of the length of gap sensing
position or placement sensors S.sub.P1 to S.sub.P5 of FIGS. 2 and
3. Sensor element 22 may employ mechanical contact, or optical,
sonic or other suitable means to accomplish measurement of the gap
which may range from substantially zero to one-half inches.
Position transducer 22, for example, may be a linear potentiometer
having a mechanical roller which is carried by its slider and urged
yieldably into contact with rail 2 whereby the potentiometer is
adjusted as the roller and slider are moved in response to any
changes in the motor-to-rail gap as the roller rides along the
rail. Motor 1 and rail 2 represent the various motor and rail
combinations disclosed in FIGS. 2 and 3, and the potentiometer may
be suitable carried either by the vehicle or on the particular
motor with which it is used.
An optical displacement sensor 22 may be arranged with a photocell
on one side of the motor-rail gap and illumination means on the
other so that more or less light is caused to enter the photocell
to change its electrical response as a function of gap length.
An ultra-sonic sensor 22 may be arranged to produce ultra-sonic
sound reflections from the rail so that detected changes in phase
of the transmitted and reflected sound may provide a suitable
measure of gap length and changes therein.
Signals from position transducer 22 are supplied to a compensating
network 23 and also to a multiplier 25, subsequently to be
described.
Compensating network 23 provides an adjustable reference for the
gap measurement in electrical terms, that is to say, this reference
may be adjusted to preset a selected gap which the position sensor
will seek. The compensating network 23 also has provision for
adjusting its position signal to zero for a selected gap, or to
some strength other than its normal signal for that gap for
purposes of the FIG. 3 vehicle guidance operation, aforedescribed.
The compensating network 23, moreover, has provision for receiving
signals from the accelerometer sensors S.sub.A4 and S.sub.A5 of
FIG. 2 to provide banking adjustment of gaps l.sub.1 and l.sub.2,
as aforedescribed. Network 23, in addition, provides velocity and
integrated displacement feedback. Integration is performed over a
range of frequencies from 0 to about 1.2 hertz, and differentiation
is performed over a range of frequencies from 1.2 to about 5
hertz.
Signals from the compensating network 23 pass to compensating
network 21 where they are combined, that is, are algebraically
summed with the acceleration signals for common amplification to
provide a force-proportional voltage representative of the function
F.sub.M in equation (4). This force-proportional voltage operates
in the whole feedback system to enable motor 1 to produce a
magnetic force F.sub.M of 1 g, that is, an equal and opposite force
in relation to gravity whereby the motor-vehicle mass is
magnetically suspended.
As hereinbefore discussed, the magnetic force F.sub.M is
proportional to the square of the motor current which is a
non-linear relationship which must be linearized in order to
provide feedback stability. Linearization is achieved by taking the
square root of the force-proportional voltage output of network 21
in accordance with the mathematical requirement expressed by the
function .sqroot.F.sub.M in equation (4).
This required square-rooting of the force-proportional voltage
output of network 21 is performed by the square-root circuit 24
which is typically an operational amplifier entity employing
non-linear transistor characteristics to give an electrical output
that is the equivalent of the square-root of the electrical
input.
The length of gap and square-root outputs of position transducer 22
and square-root circuit 24 are applied as first and second inputs
to multiplier 25 and multiplied thereby to provide a product which
corresponds to the product requirement .sqroot.F.sub.M .times. lR
of equation (4). Multiplier 25 is an operational entity whose
output is the product of two electrical inputs, and it thus
provides an output voltage that increases with gap length. The
electrical path through multiplier 25 is independent of frequency
so that an output is produced thereby at zero frequency which is
the condition when the gap length is constant between the motor 1
and rail 2.
The output of square-root circuit 24 is also applied to perfect
differentiator 26 which is an amplifier having a
resistance-capacitance circuit to perform electrical
differentiation and thus provide the first derivative of its input
over a frequency from substantially zero to 200 hertz. The
capacitor is not shunted by any conductive path and so the output
of the differentiator is zero for zero frequency, that is, for
d.c., which is the condition when the motor-to-rail gap is
constant. The amplifier-differentiator circuit of perfect
differentiator thus produces and provides an a.c. path for the
voltage which represents the reactive component j.sqroot. F.sub.M
.times. K.sub.4 .omega. of equation (4). The output of
differentiator 26 thus provides a voltage which increases with the
feedback frequency, that is, the frequency of the sensed
signals.
The outputs from multiplier 25 and differentiator 26 are summed
algebraically to provide to the input of amplifier 95 a feedback
control voltage which represents the sum of the resistance and
reactance voltage components of equation (4), namely,
.sqroot.F.sub.M lR + j.sqroot.F.sub.M K.sub.4 .omega.
or
.sqroot.F.sub.M (lR + jK.sub.4 .omega.).
After amplification at level raising amplifier 95, and gain setting
potentiometer 96, the feedback control voltage is applied to the
controllable power supply 38 which is a power amplifier of the
Class B type for low power output of about one kilowatt or of the
Class D type or gated-silicon-controlled-rectifier type for higher
power outputs. The basic source of power for these amplifiers, for
example, is an external power supply 39 having 3rd rail connections
39' with the vehicle V.
Controllable power supply 38 provides the terminal voltage E
applied to motor 1 to develop the magnetic attraction force
F.sub.M. The combined gains of potentiometer 96 and the voltage
gain of amplifier 38 determines the constant K.sub.3 in equation
(4) such that the motor terminal voltages becomes:
E = K.sub.3 .sqroot.F.sub.M (lR + jK.sub.4 .omega.)
which is equation (4).
The motors may be built in a large range of sizes, but as an
example, for a 30 inch long motor capable of supporting 2,000
pounds, the several aforementioned constants may have values
expressed in inches as follows:
K.sub.1 = 0.48 K.sub.2 = 0.1 K.sub.3 = 2.1 K.sub.4 = 0.1.
Referring now to FIG. 4A, accelerometer 20 is a piezoelectric
accelerometer of the Endevco type 2200 and is shown to have a mass
40 of appreciable magnitude which is so disposed on the vehicle V
or on motor 1 of FIG. 4 so as to be sensitive to vertical
acceleration to thus enable the accelerometer to perform its
required feedback functions, as aforedescribed, as well as to
provide the "soft" ride features which characterize this
invention.
Amplifier entities 41, 42 and 43 comprise elements of compensating
network 21.
Amplifier 41 is a known impedance-matching amplifier and is
required to reduce the very high impedance of a piezoelectric
accelerometer to an ordinary circuit value. The amplifier is a
Motorola MC 1456G integrated circuit amplifier, or an equivalent
operational amplifier. It is connected as a source-follower and has
no gain, nor phase shift. The input circuit includes resistor 44,
of 250 megohms resistance, connected from amplifier terminal 3 to
ground to provide an input bias current path for the amplifier.
This is shunted by capacitor 45, of 1,000 picofarads (pf)
capacitance, which acts as a padding capacitor to the stray
capacitance of the input lead from the accelerometer to terminal 3.
The several terminals of the integrated circuits, operational
amplifiers, etc. have been given small numerals, corresponding to
those given by the manufacturer on the device itself. The internal
circuits for these devices are known from the manufacturer's
catalogs.
Amplifier 41 has a feedback circuit between its terminals 6 and 2
comprised of a 250 megohm resistor 46, shunted by capacitor 47, of
1,000 pf capacitance. Terminal 7 is connected to a direct current
energizing power source having a voltage of the order of + 15
volts, while terminal 4 is connected to a similar source having the
opposite polarity of - 15 volts. Each of these connections is
filtered by a 0.1 microfarad (.mu.f) capacitor connected therefrom
to ground.
Capacitor 48, of 200 .mu.f capacitance, is connected to the output
terminal 6 of amplifier 41 to restrict the low frequency signal
amplitude from the accelerometer with a roll-off starting at 0.13
hertz. This removes the "noise" from the accelerometer circuit at
low frequencies. Resistor 49, of 6,800 ohms, connected in series
with capacitor 48 and with resistor 50, of 0.2 megohms, sets the
accelerometer channel gain. Amplifier 42 provides an accelerometer
channel gain of 200/6.8 = 30. The second terminal of resistor 49
connects to input terminal 2 of amplifier 42, a Motorola MC 1741CG
integrated circuit or equivalent.
There is also another connection to terminal 2; from the output of
the gap-length sensor circuit, to be later described.
Amplifier 42 functions as a simple amplifier, having a feedback
circuit connected between input terminal 2 and output terminal 6
comprised of resistor 50, of 20 K ohms, shunted by capacitor 51, of
1,500 pf. The voltage supply and grounding connections are standard
and are known. The gain of amplifier 42 is approximately 30, up to
an upper cut-off frequency of 8 hertz.
The algebraically summed signals from the accelerometer and
gap-sensor now pass into terminal 2 of amplifier 43, of MC 1741G
type, through resistor 53, of 30,000 ohms resistance, which is used
for gain setting. The feedback circuit of amplifier 43 is the same
as that of amplifier 42; i.e., resistor 50' of 0.2 megohm and
capacitor 55 of 0.2 microfarad. Supply circuits are conventional.
The gain of amplifier 43 is approximately 7, with an upper cut-off
frequency of 4 hertz.
Capacitor 55 acts as a partial integrator upon the acceleration
feedback signal. This provides a quasi-velocity feedback signal and
prevents an oscillatory condition otherwise existing because of an
180.degree. phase shift between acceleration and displacement. This
is effective from a frequency of the order of 10 hertz down to 4
hertz. Below 4 hertz differentiation of the position (displacement)
feedback occurs to provide the velocity component. This is produced
by capacitor 58 in the input circuit to amplifier 61, hereinafter
to be described.
The combination of these two signals gives control of the phase of
the feedback circuit so that displacement information can be fed
into a system that has feedback from an accelerometer included in
it. Actually, four aspects of feedback are present in the system to
give a high degree of stability; the integral of displacement to
bring the system back to a mean gap length after load changes in
the vehicle, displacement feedback to stabilize the integral
displacement feedback circuit, velocity feedback to stabilize and
damp the displacement feedback, and acceleration feedback to
stabilize and damp the velocity feedback. At the same time the
acceleration feedback corrects second order non-linearities in the
linearizing circuit comprised of square-root circuit 24, multiplier
25, and differentiator 26. This mode of operation is required for
any system of the nature of a magnetically supported railroad,
where the air-gap length is purposely allowed to vary to
accommodate "rough track." The gap is brought back to a mean value
gradually, to provide a "soft" ride.
Position transducer 22 is shown to be a potentiometer 56 connected
to ground and shunted by a source of voltage such as battery 57.
Its slider or wiper carries the aforedescribed
rail-engaging-roller, not shown. Typically, battery 57 may have a
voltage of 10 volts and the travel of the slider have a travel of
one-half inch. This range of travel normally covers the operating
change in the length of the air gap, the preferred length of which
is one-quarter inch or perhaps slightly less. These constants give
a voltage of 20 times l; i.e., 20 times the length of the air gap
as measured in inches. Battery 57 may, alternately, be a regulated
power supply of the same voltage.
The output from position transducer element 22 passes to
compensating network 23. Capacitor 58, of 0.1 .mu.f, in series with
resistor 59, of 4,700 ohms, all shunted by resistor 60, of 1.5
megohms, are the initial elements of compensating network 23. This
network has a resistive impedance of 1.5 megohms from d.c. to 1.2
hertz, decreasing to about 4,700 ohms at 350 hertz. This provides a
velocity signal (i.e., differentiated displacement) at frequencies
above 1.2 hertz.
This output passes to input terminal 2 of operational amplifier 61,
an MC 1741G type. Both input terminals 2 and 3 of this amplifier
are individually returned to ground through resistors 62 and 63, of
22,000 ohms, to provide a path for the input bias currents of this
amplifier.
The feedback circuit for amplifier 61 is comprised of resistor 64,
10,000 ohms, in series with capacitor 65, 100 .mu.f; with resistor
66, 100,000 ohms, shunted across the capacitor. This gives an
impedance of 110,000 ohms for d.c. and of 10,100 ohms at 14 hertz,
approximately. This results in the gain of amplifier 61 at
frequencies below 1 hertz being considerably greater than at higher
frequencies. This is to increase the loop gain at low frequencies
and to provide an integral of displacement function as a feedback
signal to gradually correct for changes in load.
Since the purpose of the feedback system is to correct for changes
in loading of the vehicle, wind pressure and unevenness of the
track, the frequency of the feedback signals is very low with
respect to the frequencies handled by usual electrical networks.
Feedback must be maintained at zero frequency (d.c.). The range of
frequencies of maximum interest extends from 0 to 5 hertz for the
displacement channel and from 0.3 to 30 hertz for the accelerometer
channel.
Potentiometer 67, of 50,000 ohms total resistance, is connected
between positive and negative voltage supply sources, each of which
has a voltage of 15 volts with respect to ground. Bypass
capacitors, of 50 .mu.f, are provided from each to ground to remove
extraneous variations, as known. Potentiometer 67 provides a
voltage adjustment for any initial offset voltage in amplifier 61.
Its slider is connected to input terminal 3 thereof, through
isolating resistor 67' of 1 megohm.
An additional input to terminal 3 of amplifier 61 is from
potentiometer 68, of 2,000 ohms, and passes through attenuating
resistor 68' of 1.5 megohms, to provide a reference displacement
proportional voltage. Amplifier 61 generates an output voltage
proportional to the difference between the voltage reference input
to resistor 68' and the input to resistor 60, which is the voltage
from displacement transducer 22. Voltage dropping resistor 69,
connected in series with potentiometer 68 from the positive voltage
connection to ground, typically has a resistance value half as
great as the resistance value of potentiometer 68.
The output of amplifier 61, from terminal 6, passes to terminal 2
input of amplifier 42 through resistor 66', of 22,000 ohms, a
summing resistor. It is at this point that compensating network 23
joins that of 21, for the inclusion of amplifiers 42 and 43 in
common. The output from amplifier 43 is taken from terminal 6 and
passes through diode 54 with the cathode thereof connected to the
terminal so that only negative signal variations will be passed on.
Additionally, diode 52 is connected as a feedback element on
amplifier 43 to prevent positive voltage excursions.
Only negative voltages are allowable at the input of the
square-root circuit which follows because inversion therein to
positive signal polarity occurs before the square-root function
takes place. This prevents taking the square-root of negative
numbers, which are imaginary. Herein the square-root circuit
becomes inoperative because feedback of positive polarity drives it
to current saturation.
The force-proportional voltage output at amplifier 43 is made to be
linearly proportional to a force between the load mass and the
rail. Referring to equation (4), to develop the proper voltage E to
be applied to the motor windings, the force-proportional voltage is
to be square-rooted and multiplied by (lR + jK.sub.4 .omega.).
The first electrical device to significantly execute the
mathematics of linearization is the square-root circuit 24. This
may be an integrated circuit 24', of type MC 1494L (Motorola)
normally known as a "multiplier" of electrical signals fed into it.
This multiplier is placed in the feedback circuit of an operational
amplifier 70 and the square-root of the signal input is provided
therefrom. The theory and practice of this square-root performance
is known, being set forth in the (Motorola) manufacturer's,
"Specifications and Applications Information," October 1970 -- DS
9163. Operational amplifier 70 may be an MC1741G integrated
circuit.
The output from the previously mentioned diode 54 is connected to
gain-setting resistor 71, of 52,000 ohms, and also to ground
through resistor 72, of 1,000 ohms. The latter resistor provides a
path for any leakage current in diode 54. The input from resistor
71 is connected to terminal 14 of multiplier 24' and also to
terminal 2 of amplifier 70. The output of this amplifier, at
terminal 6, is connected to terminals 9 and 10 of the multiplier
and also to ground by a small capacitor 73, of 10 pf capacitance,
in series with resistor 74, of 510 ohms. Zener diode 75 is also
connected between the output of amplifier 70 and ground to prevent
accidental latch-up (malfunctioning) of the circuit. A type 1N5241
may be used.
The feedback path for amplifier 70 is the multiplier 24' connected
between input terminal 2 and output terminal 6 of amplifier 70 and
terminals 9 - 10 and 14 of the multiplier. Capacitor 76, of 10 pf
capacitance, is connected between amplifier terminals 2 and 6 for
the purpose of phase-compensating the amplifier. Input terminal 3
thereof is connected to the slider of potentiometer 77, which
potentiometer has a resistance of 20,000 ohms. This provides a
voltage reference for the amplifier. This potentiometer is
connected in parallel with a duplicate potentiometer 78, which is
connected between terminals 2 and 4 of multiplier 24'. A resistor
79, of 62,000 ohms, and a resistor 80, of 30,000 ohms, are
respectively connected between terminals 7 and 8 and 11 and 12 of
multiplier 24'; and a resistor 81, of 16,000 ohms, is connected
between terminal 1 and ground. A voltage source, typically of 15
volts of positive polarity, is connected respectively to terminals
7 and 15 of the amplifier and multiplier, whereas a voltage source
typically of 15 volts of negative polarity, is respectively
connected to terminals 4 and 5 of the amplifier and multiplier.
At the input to the square-root circuit 24, a negative signal
voltage of 4 volts produces in the whole system a force of 1 g;
that is, there is produced an equal an opposite force in relation
to that of gravity, whereby the motor-vehicle mass is magnetically
suspended. With the connections and voltages given, the output of
the square-rooter circuit 24 at terminal 6 of amplifier 70 is the
square-root of 10 times the input. This is the square-root of 10 in
effective amount and is taken into consideration in establishing
the whole feedback gain. Mathematically, such functioning of the
electrical circuits is accounted for in the values of the several K
constants.
The output from the square-root circuit is connected to the input
of multiplier 25 to perform the lR portion of equation (4), and
also to the input of perfect differentiator 26 to perform the
jK.sub.4 .omega. term. The input to multiplier 25 is terminal 10 of
multiplier 25' and to the perfect differentiator is capacitor 83
through resistor 90.
The above input to the multiplier may be termined the x input. The
y input is connected to input terminal 9 and comes directly from
potentiometer 56 of position sensor 22 through resistor 84 for
isolation. The resistance value of resistor 84 may be 0.1 megohm.
Both input terminals 10 and 09 are also connected to ground through
capacitors 85 and 85', of 10 pf capacitance, in series with
resistors 86 and 86', of 510 ohms resistance, respectively. These
prevent high frequency parasitic oscillations.
Resistors 79', 80' and 81' are identical in resistance value and
connection to multiplier unit 25' as these were with respect to
unit 24' of square-root circuit 24. So also are potentiometers 77'
and 78', except that the resistance value of potentiometer 77' is
50,000 ohms. An additional potentiometer 87, of 20,000 ohms, is
connected across terminals 2 and 4 of units 25', with the slider
connected to terminal 6. These three potentiometers are adjusted to
give proper x, y and output offset bias, as outlined in the
manufacturer's "Specification and Application Information"
previously referred to.
An MC 1741G operational amplifier 89 coacts with multiplier unit
25' to give the complete multiplier 25. Feedback capacitor 76', of
10 pf, is connected to the amplifier at terminals 2 and 6, and is
shunted by resistor 88, of 52,000 ohms. Positive and negative
voltage supply sources are as previously described.
Perfect differentiator capacitor 83 has a capacitance of 0.2 .mu.f.
It is in series with resistor 90, of 1,000 ohms resistance. The
capacitor connects to input terminal 2 of operational amplifier 91,
which may be a MC 1741G type. The feedback circuit of this
amplifier is comprised of capacitor 92, of 0.0068 .mu.f, and
resistor 93, of 0.1 megohm, in parallel and connected between
amplifier terminals 2 and 6. Second input terminal 3 is grounded.
Positive power supply voltage is connected to terminal 7, while the
same in negative polarity is connected to terminal 4. This
amplifier-differentiator provides the first derivative of the input
over a frequency range of from essentially zero to 200 hertz.
The output from amplifier 91 is taken through summing resistor 94,
of 62,000 ohms, to input terminal 2 of amplifier 95. The latter
mainly raises the signal level, after providing for the summing,
for parallel feeding all of the three-phase multipliers that
follow. Similarly, the output from multiplier operational amplifier
89 is taken through summing resistor 94', of 62,000 ohms, and
connects to input terminal 2 of amplifier 95. This provides the
total electrical representation of .sqroot.F (lR + jK.sub.4
.omega.) of equation (4).
The feedback circuit 92', 93' of amplifier 95 is the same as the
feedback circuit 92, 93 of amplifier 91; also, input terminal 3 is
connected to ground and the power supply connections are the same
as for amplifier 91.
The output at terminal 6 of amplifier 95 passes to potentiometer
96, which is grounded, as shown. The slider of the potentiometer is
connected to the controllable power amplifier 38 of FIG. 4 which
provides a motor terminal voltage and motor current which, in turn,
produces a magnetic force F.sub.M equal to 1 g when a negative
voltage input to the square root circuit is 4 volts.
Considering operative details of the feedback circuits of FIGS. 4
and 4A which are designed to provide a "smooth" ride in the
transportation of people, adjustment of the suspension gap length l
is accomplished by varying the voltage at input 3 of amplifier 61,
as determined by the setting of potentiometer 68. The gain of
amplifier 41, of course, is unity. The gain of amplifier 42 is
approximately 30, up to an upper cut-off frequency of 8 hertz. The
gain of amplifier 43 is approximately 7, with an upper cut-off
frequency of 4 hertz. When the output of this amplifier is -4
volts, the force exerted by motor 1 is 1 g; i.e., the vehicle is
suspended.
In forming the feedback circuits according to this invention use is
made of the fact that the a.c. flux density in the motor to rail
air-gap does not vary if the length of the gap changes. This flux
density is affected only by the value of the volts-per-turn in the
magnetic structure, and so the voltage only in any given magnetic
structure. Multiplier 25 provides compensation for d.c. flux
density changes with change in the length of the air-gap. Position
transducer element 22 senses the d.c. gap length and the gain of
the feedback circuit is modulated to increase with gap length,
maintaining the overall system gain, including the characteristics
of motor 1, constant.
In a typical motor the inductive reactance of the coils is equal to
the resistance of the coils at a frequency of the order of 2 hertz.
The inductance varies inversely with the length of the air-gap.
Proper feedback performance is maintained, however, by provision of
the d.c. path through multiplier 25 and the a.c. path through
perfect differentiator 26. The exciting current through the motor
coils increases with gap length, thus the d.c. flux remains
constant.
In practical operation, this necessary mode of operation requires
that extended periods of suspension at long air-gaps cannot be
allowed. It is good practice to rate the amplifiers comprising
controlled power supply 38 for the average length of gap
encountered and to return the vehicle to that length within a few
seconds without causing an artificial jolt after a gap-lengthening
perturbation.
The force exerted magnetically by the motor in providing suspension
varies as the square of the current in the windings of the motor.
This is a non-linear relation. Non-linear elements in the feedback
circuit, such as the square-root circuit 24 of FIGS. 4 and 4A make
the output of the feedback circuit linear, from a voltage input to
a force output. This results in a constant feedback loop gain at
all values of alternating current frequency and at all gap lengths
of the motor to the rail. Moreover, this results in a uniform
easiness of ride. A typical variation of gap may extend from + 100
percent to nearly - 100 percent of a normal value of 1.0 inch. To
prevent the motor from actually contacting the rail, a flat
automotive type brake shoe may be arranged to bear upon the rail
instead, as a safety measure.
Because an inertial reference, accelerometer 20, is used in the
vertical plane, the feedback circuit ignores small track
irregularities and does not pass them on to the passengers in the
form of vibration or quick jolts. Only a mean gap is maintained by
the displacement (position) transducer 22.
Referring again to the FIG. 4A showing of compensating network 23,
a selected gap l for suspension would normally be set by adjustment
of potentiometer 68. If the same magnetic forces involved in
suspension are applied laterally as in FIG. 3, and the motors
M.sub.4, M.sub.5 therein have selected gaps which are equal, the
magnetic forces F.sub.M4 and F.sub.M5 will be equal and opposite
and each have a magnitude corresponding to their equal gaps
determined by adjustment of their respective potentiometers 68.
When it is desired that the forces F.sub.M4 and F.sub.M5 be
generated only upon deviations from the equal gaps, offset voltage
adjusting potentiometer 67 is set to reduce the voltage applied to
input terminal of amplifier 61 to zero.
When it is desired that some magnetic coupling between the rails
R.sub.4 and R.sub.5 and motors M.sub.4 and M.sub.5 be maintained at
all times, as for increased stability in guidance control
notwithstanding the accompanying magneti drag, or to provide
propulsion, the potentiometers 67 for the respective motors may be
set at some suitable value to provide strengths F.sub.M4 and
F.sub.M5 which are greater than zero at equal gap settings.
For purposes of achieving banking of the vehicle V shown in FIG. 2,
banking control channels for accelerometer sensors S.sub.A4 and
S.sub.A5 respectively comprise its accelerometer and an amplifier
such as amplifier 41 together with its associated input and output
circuit elements. In such case, the output resistor 49 of each
banking control channel is connected as shown in FIG. 4A to the
slider of potentiometer 67. Any input from the banking channel will
thus alter the gap as long as the lateral turning force sensed by
its accelerometer persists.
Reference is now directed to FIGS. 5 and 6 which disclose the
preferred embodiment of a complete feedback circuit for controlling
both the suspension and propulsion of a tracked vehicle-linear
electric motor system such as disclosed in FIG. 2.
Referring first to FIGS. 5 and 2, the accelerometer 20, as before,
provides a signal proportional to an upward or downward inertial
force acting on the vehicle V. The position transducer 22, as
before, provides a signal proportional to the length of the
motor-to-rail gap l.
The frequency compensating networks 21' and 23' have generally the
same composition as their counterpart circuit networks 21 and 23,
of FIG. 4, and function, moreover, generally in the same manner to
produce at the output of network 21' a force-proportional voltage
which represents the quantity F.sub.M in equation (4). When this
voltage is a negative 4 volts, the terminal voltage at the motor
windings is just sufficient so that the motor produces a suspension
force F.sub.M of 1g.
Square root circuit 24" also has generally the same composition and
functions generally in the same manner as its counterpart element
24 in FIG. 4 whereby the square root of the force-proportional
voltage represented by .sqroot.F.sub.M in equation (4) is provided
in its output.
For the purposes of explaining the feedback circuit arrangement of
FIG. 5 and its manner of functioning to perform the summations and
multiplications required by equation (4), this equation preferably
is expressed in the form:
E = K.sub.1 .sqroot. F.sub.M (lR + jK.sub.2 f) (9) =K.sub.1
.sqroot. F.sub.M lR + jK.sub.1 .sqroot. F.sub.M (9A) b.2 f
where:
j represents the reaction symbol
f is the propulsion frequency
K.sub.1 and K.sub.2 have constant values hereinafter to be
described.
The multiplications and product summations involving the
square-root quantity .sqroot.F.sub.M as set forth in equation (9)
are performed in a frequency control channel presently to be
described. This channel comprises speed control 30, three phase
variable frequency oscillator 31, multipliers 120 to 122 and 135 to
137, and differentiators 143 to 145.
Speed control 30 controls the frequency of oscillator 31 which
preferably provides the three phase voltages .phi.A, .phi.B and
.phi.C, although any number of phases from two upward may be used.
The three phases typically are separated by 120 electrical degrees
in time, and the circuits and windings 111, 112 and 113, FIG. 6B,
are typically "star" (i.e., "Y") connected. Oscillator 31 supplies
alternating current at constant amplitude and essentially of
sinusoidal shape over a frequency range from zero frequency at
standstill to a low audio frequency of the order of 80 hertz at
high speed.
When the system is in operation at standstill and zero frequency,
each phase of the oscillator is required to produce an output to
enable the feedback circuit to provide the suspension magnetic flux
in the motor-to-rail gap. It will be understood, however, that the
system may be operated at standstill at any frequency providing at
least one of the three phase windings is disconnected so that the
moving field required for propulsion is not established, and at
least one of the phased circuits is in operation to enable the
feedback circuit to develop the suspension flux.
Oscillator 31 may be comprised of three mechanically driven
sine-wave-generating potentiometers to provide relatively low
frequencies, the potentiometers being rotated by hand for testing
or by a geared-down variable speed motor for relatively low speed
transport use. In such case, speed control 30 is a rotatable shaft,
hand or motor driven, having three potentiometer sliders attached
thereto and angularly spaced apart from each other thereon by 120
electrical degrees. The potentiometers are of circular
configuration and suitable for full and repeated rotation of the
sliders thereon. The potentiometers preferably are wound to provide
sinusoidal voltage variations with rotation of the sliders, the
three phase output being provided therefrom when a d.c. source is
applied across the potentiometers connected electrically in
parallel.
Oscillator 31, alternatively, may be a function generator such as
type 120- 020-3, manufactured by the Wavetek company of San Diego,
Calif. Such oscillators are voltage responsive, the frequency
output increasing with the input voltage. In such case the speed
control device 30 may be a potentiometer.
The three phase output from oscillator 31, namely, phased voltages
.phi.A, .phi.B & .phi.C, are applied as the X inputs to
multipliers 120, 121 and 122, respectively, the aforementioned
square root voltage from the square-root circuit 24" being applied
to the Y inputs thereof. The resulting product output of each of
these multipliers is a sinusoidal voltage having a magnitude
represented by the equation product K.sub.1 .sqroot. F.sub.M.
The outputs from multipliers 120, 121 and 122 are applied,
respectively, as the X inputs to multipliers 135, 136 and 137, the
aforementioned air gap length proportional signal from transducer
22 being applied to the Y inputs thereof. The resulting product
output of these multipliers is a sinusoidal voltage having a
magnitude represented by the equation product K.sub.1 .sqroot.
F.sub.M lR. This voltage is the resistive or non-reactive component
of the feedback control voltage E of equation (9A).
It will be understood that each of multipliers 120, 121 and 122 and
135, 136 and 137 gives the product of its X and Y inputs whether or
not there is propulsion, that is, whether or not, the .phi.A,
.phi.B and .phi.C voltages are varying sinusoidally or are "frozen"
to instantaneous values at standstill. A common control is thus
exercised over the control signals and suspension is maintained
both at standstill and during propulsion.
It will also be understood that multipliers 120 to 122 and 135 to
137 have substantially the same composition and function as the
aforedescribed multiplier 25 of FIGS. 4 and 4A and thus, like
multiplier 25, are not influenced by the frequency of the signal
inputs thereto since the paths therethrough are essentially d.c.
The varying frequency of the X inputs to the multipliers will thus
have no effect on the magnitude of their outputs, and the frequency
can be varied as required for vehicle speed control without
affecting the feedback voltage control required to maintain
suspension.
The impedance of the motor windings, however, increases with
frequency, as before discussed, and it is necessary therefore to
increase the feedback voltage E accordingly so that the motor
current will be of the proper strength to keep the suspension flux
constant at all motor speeds. This increase in control voltage E as
a function of propulsion frequence and speed, is provided by
differentiators 143 to 145 which are connected in parallel across
their associated multipliers 135 to 137, that is, the
differentiators also receive the X input signals to their
respective multipliers and supply their outputs to the inputs of
the multiplier amplifiers, as will more fully appear in the
description of the circuit details of FIG. 6B.
Differentiators 143 to 145 have generally the same composition and
function generally in the same manner as perfect differentiator 26
of FIGS. 4 and 4A. Thus, each of these differentiators provides
only an a.c. path therethrough and an output which is a first
derivative of the input over a range of frequencies determined by
the values of its resistance-capacitance. In the case of
differentiators 143 to 145, the voltage output thereof, represented
by the reactive voltage component K.sub.1 .sqroot. F.sub.M K.sub.2
f of equation (9A), will increase with frequency from zero to about
700 hertz, being zero to zero frequency.
A significant feature and arrangement of the feedback circuit of
the present invention is that the increased voltage function
provided by the differentiators to compensate for the increase in
motor impedance with propulsion frequency does not affect the
operations of the multipliers which are performed at voltage levels
which vary only as required to support suspension, such variations
being well within the dynamic response range of the multipliers.
The dynamic response range of the differentiators, on the other
hand, may be provided fully adequate to accommodate the large
voltage increases imposed by the vehicle speed requirements.
The respective multiplier and differentiator outputs K.sub.l
.sqroot. F.sub.M lR and K.sub.1 .sqroot.F.sub.M K.sub.2 f for each
of phases .phi.A, .phi.B and .phi.C are summed in accordance with
the requirement of equation (9A) and presented to the controllable
power supply 38' which comprises three high power amplifiers 108,
109 and 110 which respectively receive the inputs for phases
.phi.A, .phi.B and .phi.C. These amplifiers preferably are of the
Class D type such as type MCB1002 available commercially from TRW
Semiconductors, Inc. of Lawndale, Calif., or a pulse-width
switching type which uses silicon-controlled-rectifiers instead of
power transistors, such as Model Y-400642 available commercially
from the Gates Learjet Corporation of Irvine, Calif.
Amplifiers 108 to 110 respectively supply their outputs to the
phased windings 111 to 113, FIG. 6B. Wayside power for these
amplifiers comprises a 3.phi. source 39' having 3rd rail
connections 39" with controllable power supply 38'.
Referring now to FIGS. 6A and 6B for circuit details of the
suspension and propulsion control circuit of FIG. 5, and first more
particularly to FIG. 6A, the accelerometer 20, as before, has the
massive weight 40 and connects to the impedance matching network
44, 45 and amplifier 41 of compensating network 21' generally in
the same manner and for the same purpose as in the compensating
network 21 of FIG. 4 except that a pre-amplifier or first stage
amplifier 150 is interposed between the input network 44, 45 and
amplifier 41 with an additional resistor 151 providing an input
bias current path for amplifier 41.
Capacitor 48, as before, restricts the low frequency signal
amplitude from the accelerometer with a roll-off starting at 0.13
hertz. This removes the accelerometer "noise" at low frequencies.
Resistor 49, connected in series with capacitor 48 and resistor 50,
together set the accelerometer channel gain, as provided by
amplifier 42, to about 12, with a lower cut off frequency of about
0.3 hertz.
Resistors 152, 153, 53 and 50' set the accelerometer channel gain,
as provided by amplifier 43 to about 7 with an upper cutoff
frequency of about 1.7 hertz, this gain being principally set by
resistors 50' and 53 as in the FIG. 4 arrangement. The
resistance-capacitance network comprises of resistors 152 and 153
and capacitors 155, 156 and 157 provide a constant accelerometer
gain of about 7.4 (17.4 db) over the frequency range from 0.3 to
3.0 hertz. This value of inertial acceleration feedback gives the
vehicle an apparent mass of 7.4 times it actual mass over this
frequency range.
Capacitor 55 acts, as in the FIG. 4A circuit arrangement, as a
partial integrator upon the acceleration feedback signal to provide
the quasi-velocity feedback effective over the range of frequencies
from about 10 hertz down to 4 hertz. The frequency compensating
network 21' makes a second order gain correction of about 10db of
feedback to the overall feedback network over the frequency range
from about (0.13) to about 5 hertz, the feedback provided by the
frequency compensating network 23' otherwise dominating in the
frequency range from zero to about 4 hertz.
The accelerometer channel loop gain vs. frequency will become more
fully apparent from the graphical showing of FIG. 8, subsequently
to be described. The specific component values for the circuit
elements of the accelerometer and frequency compensating network
21' to provide the response represented by the graphs of FIGS. 8 to
10 are set forth in the following table:
Accelerometer Channel
20 Accelerometer Endevco Type 2200 44 Resistor 500 megohms 45
Capacitor 800 pf 150 Amplifier Philbrick/Nexu no. 1009 151 Resistor
10,000 ohms 41 Amplifier Motorola MC 1456 46 Resistor 0.1 Megohm 47
Capacitor 0.001 uf 48 Capacitor 200 uf 49 Resistor 1800 ohms 66'
Resistor 22,000 ohms 42 Amplifier Motorola MC 1741 50 Resistor
20,000 ohms 152 Resistor 475 ohms 153 Resistor 475 ohms 154
Capacitor 6.8 uf 155 Capacitor 3.3 uf 156 Capacitor 3.3 uf 53
Resistor 30,000 ohms 43 Amplifier MC 1741 Motorola 50' Resistor 0.2
megohms 52 Diode 1N411 (Sylvania) 55 Capacitor 0.47 uf
Square root circuit 24" has generally the same composition and
circuit arrangement as its counterpart circuit 24 disclosed in FIG.
4A except that the elements 73, 74 and 75 of FIG. 4A are not
employed in the circuit arrangement of FIG. 6A.
The specific component values for the circuit elements of
square-root circuit 24" are set forth in the following table:
Square-Root Circuit
24' Integrated Circuit MC1794L Motorola 54 Diode IN4148 (Sylvania)
70 Amplifier MC1456 (Motorola) 71 Resistor 51,000 ohms 72 Resistor
1,000 ohms 76 Capacitor 19 pf 77 Potentiometer 20,000 ohms 78
Potentiometer 20,000 ohms 79 Resistor 61,900 ohms 80 Resistor
30,100 ohms 81 Resistor 16,200 ohms
A position sensor 22' which may be of an eddy current type such,
for example, as that available commercially from Kaman-Science
Corp. No. KD-2300-10C is employed to provide positive potential
with respect to ground. This eddy current sensor may be used in the
circuit arrangement of FIGS. 4 and 4A in lieu of position
transducer 22 employed therein. In the use of sensor 22', the
length of air gap may be of the order of 2 inches, the normal value
of the gap in such case being 1.0 inch.
Frequency compensating network 23' has generally the same
composition and circuit arrangement as its counterpart network 23
disclosed in FIG. 4A except that terminal 3 of amplifier 61 is
grounded and terminal 2 has the position voltage output of
transducer 22' applied thereto and is returned to ground through
resistor 62 connected in series with gap setting potentiometer 161
with appropriate polarity to provide negative voltage from its
wiper W.sub.S to ground. Resistor 62 and potentiometer 161 provide
the path for the input bias currents of amplifier 61, and wiper
W.sub.S is preset in accordance with the desired operating gap. In
response to the setting of wiper W.sub.S in the selected position,
vehicle V seeks a motor-to-rail gap position in which the
difference in the voltages on terminal 2 of amplifier 61 provides
the required feedback to suspend vehicle V at the selected gap,
this operation being substantially the same as described in
connection with FIG. 4A.
The specific component values for the circuit elements of the
displacement channel are set forth in the following table:
Displacement Channel
22' Position Transducer Kaman-Science KD-2300-10C 58 Capacitor 0.1
uf 59 Resistor 4700 ohms 60 Resistor 1.5 megohms 61 Amplifier
MC1456 Motorola 62 Resistor 1.5 megohms 64 Resistor 0.36 megohms 65
Capacitor 8.4 uf 66 Resistor 3.6 megohms 160 Power Supply 10.4
volts d.c. 161 Potentiometer 1000 ohms
With reference to frequency compensating network 23', the integral
of displacement provided thereby is performed by the action of its
integrating capacitor 65, FIG. 6A. Any displacement signal from
transducer 22' differing from the reference signal on wiper W.sub.S
results in a slow voltage change across capacitor 65.
Assume, for example, that the load on vehicle V increases by 50
percent. This requires the output of amplifier 43 to change from
the aforementioned -4 volts (equivalent to 1g) to -6 volts. The
d.c. gain from the displacement transducer 22' to the amplifier 43
output is approximately equal to 155, derived as follows:
Amplifier Amplifier Amplifier 61 43 42 (Circuit elements) 50'
.times. 50 .times. 64+66 , or, 152+153+53 66' 62 (Resistance
Values) 2 .times. 10.sup.5 .times. 2.times.. 1 3.96 .times.
10.sup.6 3.095 .times. 10.sup.3 2.2 .times. 10.sup.4 = 155
approximately. 1.5 .times. 10.sup.6
After current has stopped flowing in integrating capacitor 65,
there is a resultant displacement error of:
[-4 - (-6)]/155 = 0.0129 volts
at terminal 2 of amplifier 61. Since it is assumed that 20 volts at
transducer 22' corresponds to 1 inch, as it does in the case of
transducer 22 of FIGS. 4 and 4A, then:
(1" .times. 0.0129 volts)/(20 volts) = 0.0006" = 0.6 mil error
for a 50 percent load change.
The 0.6 mil error does not integrate to zero because resistor 66 is
shunted across the integrating capacitor 65. This error is
considered to have negligible effect on the operation of the
feedback system, however, and as a practical matter, may be
ignored.
As an alternative arrangement, the gap may be maintained constant
not withstanding changes in loading by applying to the output of
amplifier 43, a load compensating voltage which is proportional to
changes in the vehicle payload. This load compensating voltage may
be produced by a transducer of a well known type such, for example,
as the type known and used in the electronic scale art. Such a
transducer would be interposed, for example, between the loaded
vehicle mass and its support motors, to thus measure the changing
load, and with its output paralleled with the output of amplifier
43, to thus compensate for any gap spacing errors due to load
variations such as resulted in the aforementioned 0.6 mil error.
Such load compensation would maintain a substantially constant gap
not withstanding loading changes, accumulations, etc.
As described in connection with the circuit arrangement of FIG. 4A,
the RC input network 58 to 60 effectively provides velocity
feedback (differentiated displacement) over the frequency range
from 1.3 to about 4 to 5 hertz, as may be seen in FIG. 8, noting
curve 180 between points 181 and 182 thereon. Curve 180 represents
the system response when the circuit elements of the acceleration
and displacement channels of FIG. 6A have the specific
aforementioned component values. It will be noted, moreover, that
the DB level of displacement feedback increases rapidly as the
frequency decreases below 1.3 hertz toward zero, that is, to the
d.c. state, this being controlled by the RC network 64 to 66 in the
feedback circuit for amplifier 61 which increases the amplifier
gain with decreasing frequency.
The relative frequency responses of the acceleration and
displacement channels may be adjusted by adjustment of the
frequency compensating networks 21' and 23' to give any desired
vertical dynamic characteristic. Thus, by changing the gain
settings provided by adjustment of the values of circuit elements
58, 59, 64, 65, and 66, various ratios of acceleration and
displacement feedback may be used, depending upon the desired
"stiffness" of the ride with respect to the rails.
In addition to the aforementioned curve 180 of FIG. 8 which
represents use of a nominal amount of position feedback, curve 183
represents a relatively large value of position feedback, and curve
184 is for a low value of position feedback as would be used for a
large high speed vehicle operating with an air gap of about 1 inch
over a relatively uneven track.
Curve 185 - 186 - 187 of FIG. 8 depicts the open loop response
through the acceleration channel, this being constant for the three
disclosed examples 180, 183 and 184 of position feedback. It may be
noted that the acceleration loop gain of 7.4 (17.4 db) is constant
over the flat curve portion 186 which covers the frequency range
from 0.3 to 3.0 hertz. This value of inertial acceleration feedback
gives the vehicle V an apparent mass of 7.4 times its actual mass
over this specified frequency range. Note also, as aforementioned,
that the acceleration channel "roll-off" in the curve portion 185
begins approximately at 0.13 hertz. Attention is further directed
to the portion 187 of the acceleration channel response which
discloses that the velocity feedback provided by this channel
extends over the frequency range of about 5 to 12 hertz.
The curves of FIG. 9 show the deviation from a preset mean gap vs.
time when the change in loading is due to an external vertical
force equal to 0.1 the vehicle weight, such loading being
continuous as by a wind gust or by a change in the number of
onboard passengers, as aforementioned. The curves 190, 193 and 194
respectively correspond to the curves 180, 183 and 184 of FIG. 8 in
that they represent responses obtainable from the same values of
relative displacement feed back. As is apparent from the showing of
FIG. 9, the displacement is the least when the value of position
feedback is the greatest, this being exemplified by curves 193 and
194 which respectively exhibit greater and lesser "stiffness" than
normal feedback curve 190. The recovery time for the normal
feedback is the least of the three examples depicted. However,
curve 193 exhibits the desired gradual return to mean gap whereas
curves 190 and 194 which permit greater deviations before
correction, show greater rates of return movement to mean gap,
i.e., the return slopes are steeper.
FIG. 10 shows the ability of vehicle V to follow a track which has
sudden change of radius of upward curvature which corresponds to a
step change of upward acceleration for the three examples of
position feedback gain. The curves 200, 203 and 204 respectively
correspond to the three values of relative displacement depicted in
FIGS. 8 and 9. The minimum gain curve 204 shows that the gap is
allowed to increase 0.6 inches greater than the nominal value of
0.4 second after the deviation occurred. The deviation rate is zero
so that the car acceleration is the same as the upward track
acceleration. This large "jerk" of the track is reduced by the
magnetic suspension to: 0.1/0.4 = 0.25 g/sec. At 0.8 second the car
is accelerating upward at 0.09 g and remains at 0.1 g 0.01 g. Curve
200 shows that the vehicle vertical acceleration is the same as the
track vertical acceleration after 0.1 second, and the high gain
curve 203 results in vehicle vertical acceleration corresponding to
track vehicle acceleration after only 0.05 second.
Referring now to FIG. 6B, it will be seen that speed control 30
comprises a potentiometer 210 to provide a variable voltage input
to the voltage controlled variable frequency three phase oscillator
31. A single pole, triple throw switch 212 connects potentiometer
210 selectively across a d.c. power supply 211 having a grounded
center tap so that the oscillator is grounded when the switch is in
the ground position, as shown, and provides positive or negative
potential to ground selectively in accordance with the setting of
the switch in the positive or negative polarity positions
thereof.
Multipliers 120 - 122 are identical and each, as may be seen by
reference to the circuit details of multiplier 120, comprises an
integrated circuit 25" and amplifier 89'. Multipliers 135 - 137 are
also identical and each, as may be seen by reference to the circuit
details of multiplier 135, comprises an integrated circuit 25'" and
an amplifier 89".
Multipliers 120 - 122 and 135 - 137 have generally the same
composition and circuit arrangement as multiplier 25 of FIG. 4A
except that the RC networks 85, 86 and 85', 86' and amplifier
feedback capacitor 76' of multiplier 25 are not used in multipliers
120 - 122 and 135 - 137.
Differentiators 143 - 145 have generally the same composition and
circuit arrangement as perfect differentiator 26 of FIG. 4A except
that differentiators 143 - 145 pass their signal outputs to the
amplifiers of the associated multipliers 135 - 137,
respectively.
Power amplifiers 108 to 110 are of any type suitable for the
purpose such as Class D amplifiers and preferably are of the Class
D type disclosed and claimed in U.S. Pat. No. 3,579,132, issued to
James A. Ross on May 18, 1971.
Power connection 39" is shown to constitute a pantograph 215 in
sliding engagement with a 3rd rail 216, it being understood that
there are three such pantograph-rail systems required, one for each
of the three phases .phi.A, .phi.B and .phi.C respectively supplied
by amplifiers 108 to 110.
The specific component values for the circuit elements of the
frequency control channel are set forth in the following table:
Frequency Control Channel
30 Speed Control Elements 210 and 211 and 212 31 Oscillator Wavetek
type 120-020-3 210 Potentiometer 1000 ohms 211 Power Supply 10
volts 212 Switch Single Pole, tripple throw 120 Multiplier Elements
25" and 89' 121 " " 122 " " 135 " Elements 25'" and 89" 136 " " 137
" " 25" Integrated Circuit MC1794L Motorola 25'" Integrated Circuit
" 81" Resistor 16,200 ohms 79" resistor 61,900 ohms 80" Resistor
10,000 ohms 87' Potentiometer 20,000 ohms 78" Potentiometer 20,000
ohms 77' Potentiometer 50,000 ohms 89' Amplifier MC 1456C Motorola
89" Amplifier MC 1456C Motorola 88" Resistor 51,000 ohms 79"'
Resistor 61,900 ohms 80'" Resistor 30,100 ohms 81'" Resistor 16,200
ohms 87" Potentiometer 20,000 ohms 78'" Potentiometer 20,000 ohms
77" Potentiometer 50,000 ohms 88" Resistor 2,400 ohms 143
Differentiator Elements 83' and 90' 144 Differentiator " 145
Differentiator " 83' Capacitor 1 uf 90' Resistor 220 ohms
The motors for vehicle V may be built in a wide range of sizes, the
length of from 10 to 50 feet and a width of motor and rail of the
order of three inches being typical. Four such motors typically
weigh 5,000 pounds and, when energized, can suspend a vehicle mass
of about 80,000 pounds. When the motors are suspending only, the
vehicle being at rest with a 1 inch air gap, 40 kilowatts of power
is consumed and the kilovolt-ampere power has the same value. As
the motor speed increases with frequency and provides propulsive
force, the kilovolt-amperes increases at a faster rate than does
the wattage loss.
Motors of high efficiency will have low winding resistance and high
inductance. The motors on the other hand will require high
frequencies for high speeds which necessitates a proportionate
increase in motor terminal voltage to compensate for the increase
in motor impedance with frequency.
The RC network of each of differentiators 143 to 145, namely,
capacitor 83' of 1 .mu.f and resistor 90' of 220 ohms provides a
voltage increase with frequency in which the voltage across the
capacitor will equal the voltage across the resistance when the
frequency reaches about 700 hertz. A reluctance motor, such as
disclosed in the aforesaid parent application, has a land and slot
distance (pole pitch) of 36 inches and will move 72 inches per
cycle, or about 300 miles per hour when the frequency is about 80
hertz. (See FIG. 7A ).
It should now be apparent that there has been provided a feedback
control system in which the terminal voltage of an
electroresponsive force generator such as an electromagnet or
linear electric motor under control of position and inertial
sensors carried thereby is caused to produce an attractive force
with respect to a coacting member sufficient to maintain the same
in controlled spacial relationship against an opposing force acting
on the force generator by itself, or with its load, such as a
vehicle.
It should also be apparent that the generated attractive force may
be produced by a magnetic force field, as shown, or by an
electrostatic, or other force field in which the force varies as
the square of the generator current and inversely as the length of
gap physically separating the force generator and the member to
which it is attracted by the force field set up between them. It
should further be apparent that whereas such force-current-space
relationship is non-linear, a non-linear feedback control circuit
has been provided in which circuit elements are employed to perform
square-rooting, multiplying, and summing functions which linearize
the voltage vs. force function to stabilize the response over a
wide range of gap lengths and feedback frequencies.
It should now be fully apparent, moreover, that such a feedback
control system, as aforedescribed, is well adapted to control the
magnetic flux of a linear electric motor to maintain the suspension
of the motor and its vehicle load in controlled spacial
relationship with respect to its support rail while also producing
alternations of the suspension flux at controlled frequencies
related to desired linear propulsive speeds of the vehicle along
the rail, including zero frequency at standstill, without exceeding
the dynamic response characteristics of the feedback circuit
elements.
With particular reference to FIG. 7A it will be noted that the
linear speed vs. frequency relationship of a synchronous reluctance
motor operated in accordance with the feedback principles of the
present invention for accelerating, coasting, and decelerating is a
single straight line passing through zero. On the other hand, in
the case of an induction motor, as depicted in FIG. 7B, the
accelerating, coasting, and decelerating functions are represented
by separate parallel straight lines of which only the coasting line
representing near zero slip passes approximately through zero
frequency and speed. Some frequency other than zero is required for
accelerating and decelerating operations at standstill and low
speeds.
* * * * *