U.S. patent application number 12/776644 was filed with the patent office on 2010-09-02 for band stop filter employing a capacitor and an inductor tank circuit to enhance mri compatibility of active medical devices.
This patent application is currently assigned to Greatbatch Ltd.. Invention is credited to Henry R. Halperin, Robert A. Stevenson.
Application Number | 20100222857 12/776644 |
Document ID | / |
Family ID | 38832247 |
Filed Date | 2010-09-02 |
United States Patent
Application |
20100222857 |
Kind Code |
A1 |
Halperin; Henry R. ; et
al. |
September 2, 2010 |
Band stop filter employing a capacitor and an inductor tank circuit
to enhance MRI compatibility of active medical devices
Abstract
A band stop filter is provided for a lead wire of an active
medical device (AMD). The band stop filter includes a capacitor in
parallel with an inductor. The parallel capacitor and inductor are
placed in series with the lead wire of the AMD, wherein values of
capacitance and inductance are selected such that the band stop
filter is resonant at a selected frequency. The Q of the inductor
may be relatively maximized and the Q of the capacitor may be
relatively minimized to reduce the overall Q of the band stop
filter to attenuate current flow through the lead wire along a
range of selected frequencies. In a preferred form, the band stop
filter is integrated into a TIP and/or RING electrode for an active
implantable medical device.
Inventors: |
Halperin; Henry R.;
(Pikesville, MD) ; Stevenson; Robert A.; (Canyon
Country, CA) |
Correspondence
Address: |
Greatbatch Ltd.
10,000 Wehrle Drive
Clarence
NY
14031
US
|
Assignee: |
Greatbatch Ltd.
Clarence
NY
|
Family ID: |
38832247 |
Appl. No.: |
12/776644 |
Filed: |
May 10, 2010 |
Related U.S. Patent Documents
|
|
|
|
|
|
Application
Number |
Filing Date |
Patent Number |
|
|
11423073 |
Jun 8, 2006 |
|
|
|
12776644 |
|
|
|
|
10123534 |
Apr 15, 2002 |
|
|
|
11423073 |
|
|
|
|
60283725 |
Apr 13, 2001 |
|
|
|
Current U.S.
Class: |
607/116 |
Current CPC
Class: |
A61N 1/05 20130101; G01R
33/288 20130101; A61B 18/1492 20130101; H03H 1/0007 20130101; A61N
1/086 20170801; A61N 1/3718 20130101; A61N 1/37 20130101; H03H
2007/013 20130101; G01R 33/287 20130101; Y10T 29/49169 20150115;
A61B 2018/00839 20130101; A61B 2090/374 20160201; G01R 33/285
20130101; H03H 7/1766 20130101 |
Class at
Publication: |
607/116 |
International
Class: |
A61N 1/05 20060101
A61N001/05 |
Claims
1. A lead wire system for use with an active implantable medical
device, the lead wire system comprising: a) an implantable lead
comprising at least one lead wire having a length extending to and
meeting with a proximal lead end and a distal lead end; b) a tank
filter as a permanently passive component circuit electrically
connected in series with the lead wire somewhere along the length
thereof, the tank filter comprising a capacitor segment having a
capacitor segment first end and a capacitor segment second end, and
an inductor segment having an inductor segment first end and an
inductor segment second end, wherein the capacitor segment first
end is electrically conductively connected to the inductor segment
first end, and the capacitor segment second end is electrically
conductively connected to the inductor segment second end; c)
wherein the inductor segment has an inductor segment inductance and
an inductor segment resistance, and the capacitor segment has a
capacitor segment capacitance and a capacitor segment resistance;
and d) wherein the inductor segment resistance, the inductor
segment inductance, the capacitor segment capacitance, and the
capacitor segment resistance result in the tank filter having a Q
wherein the resultant 3 db bandwidth is on the order of
megahertz.
2. The lead wire system of claim 1 wherein the Q of the tank filter
circuit is reduced by either reducing the Q of the inductor segment
inductance, reducing the Q of the capacitor segment capacitance, or
both.
3. The lead wire system of claim 1 wherein the inductor segment
resistance is reduced in order to increase the Q of the inductor
segment.
4. The lead wire system of claim 1 wherein the inductor segment
resistance is increased in order to reduce the Q of the inductor
segment.
5. The lead wire system of claim 1 wherein the capacitor segment
resistance is raised in order to reduce the Q of the capacitor
segment.
6. The lead wire system of claim 1 wherein the Q of the tank filter
circuit is reduced by increasing the capacitor segment
resistance.
7. The lead wire system of claim 1 wherein the Q of the tank filter
is such that the 3 db bandwidth is permanently active across a
plurality of MRI pulse frequencies.
8. The lead wire system of claim 1 wherein the tank filter circuit
is disposed at or proximate to the distal end of the lead wire.
9. The lead wire system of claim 1 wherein the tank filter circuit
is integrated into an electrode.
10. The lead wire system of claim 9 wherein electrode is selected
from the group consisting of a TIP, a RING, and a PAD
electrode.
11. The lead wire system of claim 1 wherein the inductor segment
inductance ranges from 1 and 100 nanohenries.
12. The lead wire system of claim 1 wherein the inductor segment
comprises an air wound inductor.
13. The lead wire System of claim 1 wherein the capacitor segment
capacitance ranges from 100 and 10,000 picofarads.
14. The lead wire system of claim 1 wherein the capacitor segment
comprises a ceramic capacitor.
15. The lead wire system of claim 1 wherein the lead wire has a
spiral wire structure.
16. The lead wire system of claim 1 wherein the lead wire has a
bifilar wire structure.
17. The lead wire system of claim 1 being biocompatible.
18. The lead wire system of claim 1 wherein the tank filter has an
insertion loss extending from and to points defining the 3 db
bandwidth of greater than at least 10 db.
19. The lead wire system of claim 1 wherein the 3 db bandwidth
comprises a span of frequencies within the range extending from
2.5% below a selected frequency to 2.5% above the selected
frequency.
20. The lead wire system of claim 1 wherein the inductor segment
does not comprise a ferritic material or a material with a magnetic
dipole.
21. The lead wire system of claim 1 wherein the inductor segment is
comprised of at least two series discrete inductors.
22. The lead wire system of claim 1 wherein the tank filter
comprises at least one inductor segment that is self-resonant with
its parasitic capacitance at an MRI RF pulsed frequency.
23. The lead wire system of claim 1 wherein the medical device is
selected from the group consisting of a cochlear implant, a
piezoelectric sound bridge transducer, a neurostimulator, a brain
stimulator, a cardiac pacemaker, a ventricular assist device, an
artificial heart, a drug pump, a bone growth stimulator, a bone
fusion stimulator, a urinary incontinence device, a pain relief
spinal cord stimulator, an anti-tremor stimulator, a gastric
stimulator, an implantable cardioverter defibrillator, a pH probe,
a congestive heart failure device, a pill camera, a neuromodulator,
a cardiovascular stent, and an orthopedic implant.
24. An active implantable medical device lead wire system, which
comprises: a) an implantable lead comprising at least one lead wire
having a length extending to and meeting with a proximal lead end
and a distal lead end; b) a tank filter as a permanently passive
component circuit electrically connected in series with the lead
wire and comprising a capacitor segment having a capacitor segment
first end and a capacitor segment second end, and an inductor
segment having an inductor segment first end and an inductor
segment second end, wherein the capacitor segment first end is
electrically conductively connected to the inductor segment first
end, and the capacitor segment second end is electrically
conductively connected to the inductor segment second end; c)
wherein the inductor segment has an inductor segment inductance and
an inductor segment resistance, and the capacitor segment has a
capacitor segment capacitance and a capacitor segment resistance;
d) wherein the inductor segment resistance, the inductor segment
inductance, the capacitor segment capacitance, and the capacitor
segment resistance result in the tank filter having a Q wherein the
resultant 3 db bandwidth is on the order of megahertz; and e)
wherein the tank filter is in series with the lead wire with the
capacitor segment first end and the inductor segment first end
being electrically conductively connected to the distal end of the
lead wire and the capacitor segment second end and the inductor
segment second end being electrically conductively coupled to an
electrode.
25. An active implantable medical device lead wire system, which
comprises: a) an implantable lead comprising at least one lead wire
having a length extending to and meeting with a proximal lead end
and a distal lead end; b) a tank filter as a permanently passive
component circuit electrically connected to the lead wire and
comprising a capacitor segment having a capacitor segment first end
and a capacitor segment second end, and an inductor segment having
an inductor segment first end and an inductor segment second end,
wherein the capacitor segment first end is electrically
conductively connected to the inductor segment first end, and the
capacitor segment second end is electrically conductively connected
to the inductor segment second end; c) wherein the inductor segment
has an inductor segment inductance and an inductor segment
resistance, and the capacitor segment has a capacitor segment
capacitance and a capacitor segment resistance; c) wherein the
inductor segment resistance, the inductor segment inductance, the
capacitor segment capacitance, and the capacitor segment;
resistance result in the tank filter having a Q wherein the
resultant 3 db bandwidth is on the order of megahertz; and d)
wherein the tank filter is in series with the lead wire with the
capacitor segment first end and the inductor segment first end
being electrically conductively connectable to an external portion
of a terminal pin of a hermetic seal, and the capacitor segment
second end and the inductor segment second end being electrically
conductively coupled to the proximal end of the lead wire.
26. A lead wire system for use with an active implantable medical
device, the lead wire system comprising: a) an implantable lead
comprising at least one lead wire having a length extending to and
meeting with a proximal lead end and a distal lead end; b) a tank
filter as a permanently passive component circuit electrically
connected in series with the lead wire somewhere along the length
thereof, the tank filter comprising a capacitor segment having a
capacitor segment first end and a capacitor segment second end, and
an inductor segment having an inductor segment first end and an
inductor segment second end, wherein the capacitor segment first
end is electrically conductively connected to the inductor segment
first end, and the capacitor segment second end is electrically
conductively connected to the inductor segment second end; c)
wherein the inductor segment has an inductor segment inductance and
an inductor segment resistance, and the capacitor segment has a
capacitor segment capacitance and a capacitor segment resistance;
and d) wherein the inductor segment resistance, the inductor
segment inductance, the capacitor segment capacitance, and the
capacitor segment resistance result in the tank filter being tuned
to a resonant center frequency and having a 3 db bandwidth in the
Megahertz frequency range.
27. The lead wire system of claim 26 wherein the resonant center
frequency is an MRI pulsed RF frequency.
28. A lead wire system for use with an active implantable medical
device, the lead wire system comprising: a) an implantable lead
comprising at least one lead wire having a length extending to and
meeting with a proximal lead end and a distal lead end; b) a tank
filter as a permanently active circuit electrically connected in
series with the lead wire somewhere along the length thereof, the
tank filter comprising a capacitor segment having a capacitor
segment first end and a capacitor segment second end, and an
inductor segment having an inductor segment first end and an
inductor segment second end, wherein the capacitor segment first
end is electrically conductively connected to the inductor segment
first end, and the capacitor segment second end is electrically
conductively connected to the inductor segment second end; c)
wherein the inductor segment has an inductor segment inductance and
an inductor segment resistance, and the capacitor segment has a
capacitor segment capacitance and a capacitor segment resistance;
and d) wherein the inductor segment resistance, the inductor
segment inductance, the capacitor segment capacitance, and the
capacitor segment resistance result in the tank filter having a Q
wherein the resultant 3 db bandwidth is on the order of megahertz.
Description
CROSS-REFERENCE TO RELATED APPLICATIONS
[0001] This application is a continuation of U.S. application Ser.
No. 11/423,073, filed on Jun. 8, 2006, which is a
continuation-in-part of U.S. application Ser. No. 10/123,534, filed
on Apr. 15, 2002, which claims priority from U.S. provisional
application Ser. No. 60/283,725, filed on Apr. 13, 2001.
BACKGROUND OF THE INVENTION
[0002] This invention relates generally to novel EMI tank filter
assemblies, particularly of the type used in active medical devices
(AMDs) such as cardiac pacemakers, cardioverter defibrillators,
neurostimulators, externally worn Holter monitors and the like,
which decouple lead wires and/or electronic components of the
medical device from undesirable electromagnetic interference (EMI)
signals at a selected frequency or frequencies, such as the RF
pulsed fields of Magnetic Resonance Imaging (MRI) equipment.
[0003] Compatibility of cardiac pacemakers, implantable
defibrillators and other types of active implantable medical
devices with magnetic resonance imaging (MRI) and other types of
hospital diagnostic equipment has become a major issue. If one goes
to the websites of the major cardiac pacemaker manufacturers in the
United States, which include St. Jude Medical, Medtronic and Boston
Scientific (formerly Guidant), one will see that the use of MRI is
generally contra-indicated with pacemakers and implantable
defibrillators. See also:
[0004] (1) "Safety Aspects of Cardiac Pacemakers in Magnetic
Resonance imaging", a dissertation submitted to the Swiss Federal
Institute of Technology Zurich presented by Roger Christoph
Luchinger, Zurich 2002;
[0005] (2) "I. Dielectric Properties of Biological Tissues:
Literature Survey", by C. Gabriel, S. Gabriel and E. Cortout;
[0006] (3) "II. Dielectric Properties of Biological Tissues:
Measurements and the Frequency Range 0 Hz to 20 GHz", by S.
Gabriel, R. W. Lau and C. Gabriel;
[0007] (4) "III. Dielectric Properties of Biological Tissues:
Parametric Models for the Dielectric Spectrum of Tissues", by S.
Gabriel, R. W. Lau and C. Gabriel; and
[0008] (5) "Advanced Engineering Electromagnetics, C. A. Balanis,
Wiley, 1989;
[0009] (6) Systems and Methods for Magnetic-Resonance-Guided
Interventional Procedures, Patent Application Publication US
2003/0050557, Susil and Halperin et. al, published Mar. 13,
2003;
[0010] (7) Multifunctional Interventional Devices for MRI: A
Combined Electrophysiology/MRI Catheter, by, Robert C. Susil, Henry
R. Halperin, Christopher J. Yeung, Albert C. Lardo and Ergin
Atalar, MRI in Medicine, 2002; and
[0011] (8) Multifunctional Interventional Devices for Use in MRI,
U.S. Patent Application Ser. No. 60/283,725, filed Apr. 13,
2001.
[0012] The contents of the foregoing are all incorporated herein by
reference.
[0013] However, an extensive review of the literature indicates
that MRI is indeed often used with pacemaker, neurostimulator and
other active implantable medical device (AIMD) patients. The safety
and feasibility of MRI in patients with cardiac pacemakers is an
issue of gaining significance. The effects of MRI on patients
pacemaker systems have only been analyzed retrospectively in some
case reports. There are a number of papers that indicate that MRI
on new generation pacemakers can be conducted up to 0.5 Tesla (T).
MRI is one of medicine's most valuable diagnostic tools. MRI is, of
course, extensively used for imaging, but is also used for
interventional medicine (surgery). In addition, MRI is used in real
time to guide ablation catheters, neurostimulator tips, deep brain
probes and the like. An absolute contra-indication for pacemaker
patients means that pacemaker and ICD wearers are excluded from
MRI. This is particularly true of scans of the thorax and abdominal
areas. Because of MRI's incredible value as a diagnostic tool for
imaging organs and other body tissues, many physicians simply take
the risk and go ahead and perform MRI on a pacemaker patient. The
literature indicates a number of precautions that physicians should
take in this case, including limiting the power of the MRI RF
Pulsed field (Specific Absorption Rate--SAR level), programming the
pacemaker to fixed or asynchronous pacing mode, and then careful
reprogramming and evaluation of the pacemaker and patient after the
procedure is complete. There have been reports of latent problems
with cardiac pacemakers or other AIMDs after an MRI procedure
sometimes occurring many days later. Moreover, there are a number
of recent papers that indicate that the SAR level is not entirely
predictive of the heating that would be found in implanted lead
wires or devices. For example, for magnetic resonance imaging
devices operating at the same magnetic field strength and also at
the same SAR level, considerable variations have been found
relative to heating of implanted lead wires. It is speculated that
SAR level alone is not a good predictor of whether or not an
implanted device or its associated lead wire system will
overheat.
[0014] There are three types of electromagnetic fields used in an
MRI unit. The first type is the main static magnetic field
designated B.sub.0 which is used to align protons in body tissue.
The field strength varies from 0.5 to 3.0 Tesla in most of the
currently available MRI units in clinical use. Some of the newer
MRI system fields can go as high as 4 to 5 Tesla. At the recent
International Society for Magnetic Resonance in Medicine (ISMRM),
which was held on 5 and 6 Nov. 2005, it was reported that certain
research systems are going up as high as 11.7 Tesla and will be
ready sometime in 2006. This is over 100,000 times the magnetic
field strength of the earth. A static magnetic field can induce
powerful mechanical forces and torque on any magnetic materials
implanted within the patient. This would include certain components
within the cardiac pacemaker itself and or lead wire systems. It is
not likely (other than sudden system shut down) that the static MRI
magnetic field can induce currents into the pacemaker lead wire
system and hence into the pacemaker itself. It is a basic principle
of physics that a magnetic field must either be time-varying as it
cuts across the conductor, or the conductor itself must move within
the magnetic field for currents to be induced.
[0015] The second type of field produced by magnetic resonance
imaging is the pulsed RF field which is generated by the body coil
or head coil. This is used to change the energy state of the
protons and illicit MRI signals from tissue. The RF field is
homogeneous in the central region and has two main components: (1)
the magnetic field is circularly polarized in the actual plane; and
(2) the electric field is related to the magnetic field by
Maxwell's equations. In general, the RF field is switched on and
off during measurements and usually has a frequency of 21 MHz to 64
MHz to 128 MHz depending upon the static magnetic field strength.
The frequency of the RF pulse varies with the field strength of the
main static field where: RF PULSED FREQUENCY in MHz=(42.56) (STATIC
FIELD STRENGTH IN TESLA).
[0016] The third type of electromagnetic field is the time-varying
magnetic gradient fields designated B.sub.1 which are used for
spatial localization. These change their strength along different
orientations and operating frequencies on the order of 1 kHz. The
vectors of the magnetic field gradients in the X, Y and Z
directions are produced by three sets of orthogonally positioned
coils and are switched on only during the measurements. In some
cases, the gradient field has been shown to elevate natural heart
rhythms (heart beat). This is not completely understood, but it is
a repeatable phenomenon. The gradient field is not considered by
many researchers to create any other adverse effects.
[0017] It is instructive to note how voltages and EMI are induced
into an implanted lead wire system. At very low frequency (VLF),
voltages are induced at the input to the cardiac pacemaker as
currents circulate throughout the patient's body and create voltage
drops. Because of the vector displacement between the pacemaker
housing and, for example, the TIP electrode, voltage drop across
the resistance of body tissues may be sensed due to Ohms Law and
the circulating current of the RF signal. At higher frequencies,
the implanted lead wire systems actually act as antennas where
currents are induced along their length. These antennas are not
very efficient due to the damping effects of body tissue; however,
this can often be offset by extremely high power fields (such as
MRI pulsed fields) and/or body resonances. At very high frequencies
(such as cellular telephone frequencies), EMI signals are induced
only into the first area of the lead wire system (for example, at
the header block of a cardiac pacemaker). This has to do with the
wavelength of the signals involved and where they couple
efficiently into the system.
[0018] Magnetic field coupling into an implanted lead wire system
is based on loop areas. For example, in a cardiac pacemaker, there
is a loop formed by the lead wire as it comes from the cardiac
pacemaker housing to its distal TIP, for example, located in the
right ventricle. The return path is through body fluid and tissue
generally straight from the TIP electrode in the right ventricle
back up to the pacemaker case or housing. This forms an enclosed
area which can be measured from patient X-rays in square
centimeters. The average loop area is 200 to 225 square
centimeters. This is an average and is subject to great statistical
variation. For example, in a large adult patient with an abdominal
implant, the implanted loop area is much larger (greater than 450
square centimeters).
[0019] Relating now to the specific case of MRI, the magnetic
gradient fields would be induced through enclosed loop areas.
However, the pulsed RF fields, which are generated by the body
coil, would be primarily induced into the lead wire system by
antenna action.
[0020] There are a number of potential problems with MRI,
including:
[0021] (1) Closure of the pacemaker reed switch. A pacemaker reed
switch, which can also be a Hall Effect device, is designed to
detect a permanent magnet held close to the patient's chest. This
magnet placement allows a physician or even the patient to put the
implantable medical device into what is known as the "magnet mode
response." The "magnet mode response" varies from one manufacturer
to another; however, in general, this puts the pacemaker into a
fixed rate or asynchronous pacing mode. This is normally done for
short times and is very useful for diagnostic and clinical
purposes. However, in some cases, when a pacemaker is brought into
the bore or close to the MRI scanner, the MRI static field can make
the pacemaker's internal reed switch close, which puts the
pacemaker into a fixed rate or asynchronous pacing mode. Worse yet,
the reed switch may bounce or oscillate. Asynchronous pacing may
compete with the patient's underlying cardiac rhythm. This is one
reason why patients have generally been advised not to undergo MRI.
Fixed rate or asynchronous pacing for most patients is not an
issue. However, in patients with unstable conditions, such as
myocardial ischemia, there is a substantial risk for ventricular
fibrillation during asynchronous pacing. In most modern pacemakers
the magnetic reed switch (or Hall Effect device) function is
programmable. If the magnetic reed switch response is switched off,
then synchronous pacing is still possible even in strong magnetic
fields. The possibility to open and re-close the reed switch in the
main magnetic field by the gradient field cannot be excluded.
However, it is generally felt that the reed switch will remain
closed due to the powerful static magnetic field. It is
theoretically possible for certain reed switch orientations at the
gradient field to be capable of repeatedly closing and re-opening
the reed switch.
[0022] (2) Reed switch damage. Direct damage to the reed switch is
theoretically possible, but has not been reported in any of the
known literature. In an article written by Roger Christoph
Luchinger of Zurich, he reports on testing in which reed switches
were exposed to the static magnetic field of MRI equipment. After
extended exposure to these static magnetic fields, the reed
switches functioned normally at close to the same field strength as
before the test.
[0023] (3) Pacemaker displacement. Some parts of pacemakers, such
as the batteries and reed switch, contain ferrous magnetic
materials and are thus subject to mechanical forces during MRI.
Pacemaker displacement may occur in response to magnetic force or
magnetic torque. There are several recent reports on modern
pacemakers and ICDs that force and torque are not of concern for
MRI systems up to 3 Tesla.
[0024] (4) Radio frequency field. At the frequencies of interest in
MRI, RF energy can be absorbed and converted to heat. The power
deposited by RF pulses during MRI is complex and is dependent upon
the power (Specific Absorption Rate (SAR) Level) and duration of
the RF pulse, the transmitted frequency, the number of RF pulses
applied per unit time, and the type of configuration of the RF
transmitter coil used. The amount of heating also depends upon the
volume of tissue imaged, the electrical resistivity of tissue and
the configuration of the anatomical region imaged. There are also a
number of other variables that depend on the placement in the human
body of the AIMD and its associated lead wire(s). For example, it
will make a difference how much current is induced into a pacemaker
lead wire system as to whether it is a left or right pectoral
implant. In addition, the routing of the lead and the lead length
are also very critical as to the amount of induced current and
heating that would occur. Also, distal TIP design is very important
as the distal TIP itself can act as its own antenna wherein eddy
currents can create heating. The cause of heating in an MRI
environment is two fold: (a) RF field coupling to the lead can
occur which induces significant local heating; and (b) currents
induced between the distal TIP and tissue during MRI RF pulse
transmission sequences can cause local Ohms Law heating in tissue
next to the distal TIP electrode of the implanted lead. The RF
field of an MRI scanner can produce enough energy to induce lead
wire currents sufficient to destroy some of the adjacent myocardial
tissue. Tissue ablation has also been observed. The effects of this
heating are not readily detectable by monitoring during the MRI.
Indications that heating has occurred would include an increase in
pacing threshold, venous ablation, Larynx or esophageal ablation,
myocardial perforation and lead penetration, or even arrhythmias
caused by scar tissue. Such long term heating effects of MRI have
not been well studied yet for all types of AIMD lead wire
geometries. There can also be localized heating problems associated
with various types of electrodes in addition to TIP electrodes.
This includes RING electrodes or PAD electrodes. RING electrodes
are commonly used with a wide variety of implanted devices
including cardiac pacemakers, neurostimulators, probes, catheters
and the like. PAD electrodes are very common in neurostimulator
applications. For example, spinal cord stimulators or deep brain
stimulators can include a plurality of PAD electrodes to make
contact with nerve tissue. A good example of this also occurs in a
cochlear implant. In a typical cochlear implant there would be
sixteen RING electrodes that the position places by pushing the
electrode up into the cochlea. Several of these RING electrodes
make contact with auditory nerves.
[0025] (5) Alterations of pacing rate due to the applied radio
frequency field. It has been observed that the RF field may induce
undesirable fast pacing (QRS complex) rates. There are various
mechanisms which have been proposed to explain rapid pacing: direct
tissue stimulation, interference with pacemaker electronics or
pacemaker reprogramming (or reset). In all of these cases, it is
very desirable to raise the lead system impedance (at the MRI RF
pulsed frequency) to make an EMI filter feedthrough capacitor more
effective and thereby provide a higher degree of protection to AIMD
electronics. This will make alterations in pacemaker pacing rate
and/or pacemaker reprogramming much more unlikely.
[0026] (6) Time-varying magnetic gradient fields. The contribution
of the time-varying gradient to the total strength of the MRI
magnetic field is negligible, however, pacemaker systems could be
affected because these fields are rapidly applied and removed. The
time rate of change of the magnetic field is directly related to
how much electromagnetic force and hence current can be induced
into a lead wire system. Luchinger reports that even using today's
gradient systems with a time-varying field up to 50 Tesla per
second, the induced currents are likely to stay below the
biological thresholds for cardiac fibrillation. A theoretical upper
limit for the induced voltage by the time-varying magnetic gradient
field is 20 volts. Such a voltage during more than 0.1 milliseconds
could be enough energy to directly pace the heart.
[0027] (7) Heating. Currents induced by time-varying magnetic
gradient fields may lead to local heating. Researchers feel that
the calculated heating effect of the gradient field is much less as
compared to that caused by the RF field and therefore for the
purposes herein may be neglected.
[0028] There are additional problems possible with implantable
cardioverter defibrillators (ICDs). ICDs use different and larger
batteries which could cause higher magnetic forces. The
programmable sensitivity in ICDs is normally much higher (more
sensitive) than it is for pacemakers, therefore, ICDs may falsely
detect a ventricular tacchyarrhythmia and inappropriately deliver
therapy. In this case, therapy might include anti-tacchycardia
pacing, cardio version or defibrillation (high voltage shock)
therapies. MRI magnetic fields may prevent detection of a dangerous
ventricular arrhythmia or fibrillation. There can also be heating
problems of ICD leads which are expected to be comparable to those
of pacemaker leads. Ablation of vascular walls is another concern.
Fortunately, ICDs have a sort of built-in fail-safe mechanism. That
is, during an MRI procedure, if they inadvertently sense the MRI
fields as a dangerous ventricular arrhythmia, the ICD will attempt
to charge up and deliver a high voltage shock. However, there is a
transformer contained within the ICD that is necessary to function
in order to charge up the high-energy storage capacitor contained
within the ICD. In the presence of the main static field of the MRI
the core of this transformer tends to saturate thereby preventing
the high voltage capacitor from charging up. This makes it highly
unlikely that an ICD patient undergoing an MRI would receive an
inappropriate high voltage shock therapy. While ICDs cannot charge
during MRI due to the saturation of their ferro-magnetic
transformers, the battery will be effectively shorted and lose
life. This is a highly undesirable condition.
[0029] In summary, there are a number of studies that have shown
that MRI patients with active implantable medical devices, such as
cardiac pacemakers, can be at risk for potential hazardous effects.
However, there are a number of reports in the literature that MRI
can be safe for imaging of pacemaker patients when a number of
precautions are taken (only when an MRI is thought to be an
absolute diagnostic necessity). These anecdotal reports are of
interest; however, they are certainly not scientifically convincing
that all. MRI can be safe. As previously mentioned, just variations
in the pacemaker lead wire length can significantly effect how much
heat is generated. From the layman's point of view, this can be
easily explained by observing the typical length of the antenna on
a cellular telephone compared to the vertical rod antenna more
common on older automobiles. The relatively short antenna on the
cell phone is designed to efficiently couple with the very high
frequency wavelengths (approximately 950 MHz) of cellular telephone
signals. In a typical AM and FM radio in an automobile, these
wavelength signals would not efficiently couple to the relatively
short antenna of a cell phone. This is why the antenna on the
automobile is relatively longer. An analogous situation exists with
an AIMD patient in an MRI system. If one assumes, for example, a
3.0 Tesla MRI system, which would have an RF pulsed frequency of
128 MHz, there are certain implanted lead lengths that would couple
efficiently as fractions of the 128 MHz wavelength. It is typical
that a hospital will maintain an inventory of various leads and
that the implanting physician will make a selection depending on
the size of the patient, implant location and other factors.
Accordingly, the implanted or effective lead wire length can vary
considerably. There are certain implanted lead wire lengths that
just do not couple efficiently with the MRI frequency and there are
others that would couple very efficiently and thereby produce the
worst case for heating.
[0030] The effect of an MRI system on the function of pacemakers,
ICDs and neurostimulators depends on various factors, including the
strength of the static magnetic field, the pulse sequence (gradient
and RF field used), the anatomic region being imaged, and many
other factors. Further complicating this is the fact that each
patient's condition and physiology is different and each
manufacturers pacemaker and ICD designs also are designed and
behave differently. Most experts still conclude that MRI for the
pacemaker patient should not be considered safe. Paradoxically,
this also does not mean that the patient should not receive MRI.
The physician must make an evaluation given the pacemaker patient's
condition and weigh the potential risks of MRI against the benefits
of this powerful diagnostic tool. As MRI technology progresses,
including higher field gradient changes over time applied to
thinner tissue slices at more rapid imagery, the situation will
continue to evolve and become more complex. An example of this
paradox is a pacemaker patient who is suspected to have a cancer of
the lung. RF ablation treatment of such a tumor may require
stereotactic imaging only made possible through real time fine
focus MRI. With the patient's life literally at risk, the physician
with patient informed consent may make the decision to perform MRI
in spite of all of the previously described attendant risks to the
pacemaker system.
[0031] Insulin drug pump systems do not seem to be of a major
current concern due to the fact that they have no significant
antenna components (such as implanted lead wires). However, some
implantable pumps work on magneto-peristaltic systems, and must be
deactivated prior to MRI. There are newer (unreleased) systems that
would be based on solenoid systems which will have similar
problems.
[0032] It is clear that MRI will continue to be used in patients
with both external and active implantable medical devices. There
are a number of other hospital procedures, including electrocautery
surgery, lithotripsy, etc., to which a pacemaker patient may also
be exposed. Accordingly, there is a need for AIMD system and/or
circuit protection devices which will improve the immunity of
active implantable medical device systems to diagnostic procedures
such as MRI.
[0033] As one can see, many of the undesirable effects in an
implanted lead wire system from MRI and other medical diagnostic
procedures are related to undesirable induced currents in the lead
wire system and/or its distal TIP (or RING). This can lead to
overheating either in the lead wire or at the body tissue at the
distal TIP. For a pacemaker application, these currents can also
directly stimulate the heart into sometimes dangerous
arrhythmias.
[0034] Accordingly, there is a need for a novel resonant tank band
stop filter assembly which can be placed at various locations along
the active implantable medical device lead wire system, which also
prevents current from circulating at selected frequencies of the
medical therapeutic device. Preferably, such novel tank filters
would be designed to resonate at 64 MHz for use in an MRI system
operating at. 1.5 Tesla (or 128 MHz for a 3 Tesla system). The
present invention fulfills these needs and provides other related
advantages.
SUMMARY OF THE INVENTION
[0035] The present invention comprises resonant tank circuits/band
stop filters to be placed at one or more locations along the active
medical device (AMD) lead wire system, including its distal Tip.
These band stop filters prevent current from circulating at
selected frequencies of the medical therapeutic device. For
example, for an MRI system operating at 1.5 Tesla, the pulse RF
frequency is 64 MHz. The novel band stop filters of the present
invention can be designed to resonate at 64 MHz and thus create an
open circuit in the lead wire system at that selected frequency.
For example, the band stop filter of the present invention, when
placed at the distal TIP, will prevent currents from flowing
through the distal TIP, prevent currents from flowing in the lead
wires and also prevent currents from flowing into body tissue. It
will be obvious to those skilled in the art that all of the
embodiments described herein are equally applicable to a wide range
of other active implantable or external medical devices, including
deep brain stimulators, spinal cord stimulators, cochlear implants,
ventricular assist devices, artificial hearts, drug pumps, Holter
monitors and the like. The present invention fulfills all of the
needs regarding reduction or elimination of undesirable currents
and associated heating in implanted lead wire systems. The band
stop filter structures as described herein also have a broad
application to other fields, including telecommunications,
military, space and the like.
[0036] Electrically engineering a capacitor in parallel with an
inductor is known as a tank filter. It is also well known that when
the tank filter is at its resonant frequency, it will present a
very high impedance. This is a basic principle of all radio
receivers. In fact, multiple tank filters are often used to improve
the selectivity of a radio receiver. One can adjust the resonant
frequency of the tank circuit by either adjusting the capacitor
value or the inductor value or both. Since medical diagnostic
equipment which is capable of producing very large fields operates
at discrete frequencies, this is an ideal situation for a specific
tank or band stop filter. Band stop filters are more efficient for
eliminating one single frequency than broadband filters. Because
the band stop filter is targeted at this one frequency or range of
frequencies, it can be much smaller and volumetrically efficient.
In addition, the way MRI RF pulse fields couple with lead wire
systems, various loops and associated loop currents result along
various sections of the lead wire. For example, at the distal TIP
of a cardiac pacemaker, direct electromagnetic forces (EMF) can be
produced which result in current loops through the distal TIP and
into the associated myocardial tissue. This current system is
largely decoupled from the currents that are induced near the
active implantable medical device, for example, near the cardiac
pacemaker. There the MRI may set up a separate loop with its
associated currents. Accordingly, one or more band stop filters may
be required to completely control all of the various induced EMI
and associated currents in a lead wire system.
[0037] The present invention which resides in band stop filters is
also designed to work in concert with the EMI filter which is
typically used at the point of lead wire ingress and egress of the
active implantable medical device. For example, see U.S. Pat. No.
5,333,095, entitled FEEDTHROUGH FILTER CAPACITOR ASSEMBLY FOR HUMAN
IMPLANT; U.S. Pat. No. 6,999,818, entitled INDUCTOR CAPACITOR EMI
FILTER FOR HUMAN IMPLANT APPLICATIONS; U.S. patent application Ser.
No. 11/097,999 filed Mar. 31, 2005, entitled APPARATUS AND PROCESS
FOR REDUCING THE SUSCEPTIBILITY OF ACTIVE IMPLANTABLE MEDICAL
DEVICES TO MEDICAL PROCEDURES SUCH AS MAGNETIC RESONANCE IMAGING;
and U.S. patent application Ser. No. 11/163,915 filed Nov. 3, 2005,
entitled PROCESS FOR TUNING AN EMI FILTER TO REDUCE THE AMOUNT OF
HEAT GENERATED IN IMPLANTED LEAD WIRES DURING MEDICAL PROCEDURES
SUCH AS MAGNETIC RESONANCE IMAGING; the contents of all being
incorporated herein by reference. All of these patent documents
describe novel inductor capacitor combinations for low pass EMI
filter circuits. It is of particular interest that by increasing
the number of circuit elements, one can reduce the overall
capacitance value which is at the input to the implantable medical
device. It is important to reduce the capacitance value to raise
the input impedance of the active implantable medical device such
that this also reduces the amount of current that would flow in
lead wire systems associated with medical procedures such as MRI.
Accordingly, it is a feature of the present invention that the
novel band stop filters are designed to be used in concert with the
structures described in the above mentioned three patent
applications.
[0038] As described in U.S. Patent Publication No. 2003/0050557 and
U.S. Patent Application Ser. No. 60/283,725, the present invention
is also applicable to probes and catheters. For example, ablation
probes are used to selectively cauterize or ablate tissue on the
inside or outside of the heart to control erratic electrical
pulses. These procedures are best performed during real time
fluoroscopy or MRI imaging. However, a major concern is the
overheating of the distal TIP at inappropriate times because of the
induced currents from the MRI system. It will be obvious to one
skilled in the art that the novel band stop filters of the present
invention can be adapted to any probe, TIP or catheter that is used
in the human body.
[0039] Moreover, the present invention is also applicable to a
number of external leads that might be placed on a patient during
MRI. For example, patients frequently wear Holter monitors to
monitor their cardiac activity over a period of days. It is an
aggravation to physicians to have a patient sent up to the MRI
Department and have all these carefully placed electrodes removed
from the patient's body. Typically the MRI technicians are
concerned about leaving these leads on during an MRI because they
don't want them to overheat and cause surface burns on the
patient's skin. The problem is that after the MRI procedure, the
MRI technicians often replace these electrodes or skin patches in
different or even in the wrong locations. This greatly confounds
the cardiac physician because now the Halter monitor results are no
longer consistent. It is a feature of the present invention that
the tank filters could be placed in any externally worn lead wires
by the patient during an MRI procedure such that they do not need
to be removed.
[0040] In one embodiment, the invention provides a medical
therapeutic device comprising an active medical device (AMD), a
lead wire extending from the AND to a distal TIP thereof, and a
band stop filter associated with the lead wire for attenuating
current flow through the lead wire at a selected frequency.
[0041] The AMD may comprise cochlear implants, piezoelectric sound
bridge transducers, neurostimulators, brain stimulators, cardiac
pacemakers, ventricular assist devices, artificial hearts, drug
pumps, bone growth stimulators, bone fusion stimulators, urinary
incontinence devices, pain relief spinal cord stimulators,
anti-tremor stimulators, gastric stimulators, implantable
cardioverter defibrillators, pH probes, congestive heart failure
devices, pill cameras, neuromodulators, cardiovascular stents,
orthopedic implants, external insulin pumps, external drug pumps,
external neurostimulators, and external probes or catheters.
[0042] The band stop filter itself comprises a capacitor (and its
resistance or an added resistance) in parallel with an inductor
(and its parasitic resistance), said parallel capacitor and
inductor combination being placed in series with the medical device
lead wire(s) wherein the values of capacitance and inductance have
been selected such that the band stop filter is resonant at a
selected frequency (such as the MRI pulsed frequency).
[0043] In the preferred embodiment, the Q of the inductor is
relatively maximized and the Q of the capacitor is relatively
minimized to reduce the overall Q of the band stop filter. The Q of
the inductor is relatively maximized by minimizing the parasitic
resistive loss in the inductor, and the Q of the capacitor is
relatively minimized by raising its equivalent series resistance
(ESR) of the capacitor (or by adding resistance or a resistive
element in series with the capacitor element of the bank stop tank
filter). This reduces the overall Q of the band stop filter in
order to broaden its 3 dB points and thereby attenuate current flow
through the lead wire along a range of selected frequencies in AIMD
or external medical device applications, the range of selected
frequencies includes a plurality of MRI pulsed frequencies.
[0044] The equivalent series resistance of the capacitor is raised
by any of the following: reducing thickness of electrode plates in
the capacitor; using higher resistivity capacitor electrode
materials, providing apertures, gaps, slits or spokes in the
electrode plates of the capacitor; providing separate discrete
resistors in series with the capacitor; utilizing resistive
electrical attachment materials to the capacitor; or utilizing
capacitor dielectric materials that have high dielectric loss
tangents at the selected frequency. Methods of using higher
resistivity capacitor electrode materials include, for example,
using platinum instead of silver electrodes. Platinum has a higher
volume resistivity as compared to pure silver. Another way of
reducing capacitor electrode plate resistivity is to add ceramic
powders to the electrode ink before it is silk screened down and
fired. After firing, this has the effect of separating the
conductive electrode portions by insulative dielectric areas which
increases the overall resistivity of the electrode plate.
[0045] As defined herein, raising the capacitor ESR includes any or
all of the above described methods of adding resistance in series
with the capacitive element of the band stop filter. It should be
noted that deliberately raising the capacitor ESR runs counter to
conventional/prior art capacitor technologies. In fact, capacitor
manufacturers generally strive to build capacitors with as low an
ESR as possible. This is to minimize energy loss, etc. It is a
feature of the present invention that capacitor Q is raised in a
controlled manner in the tank filter circuit in order to adjust its
Q and adjust the band stop frequency width in the range of MRI
pulsed frequencies.
[0046] Preferably, the band stop filter is disposed adjacent to the
distal tip of the lead wire and is integrated into a TIP electrode.
It may also be integrated into one or more RING electrodes. The
lead wire may also comprise an externally worn lead wire, or it may
come from an externally worn electronics module wherein said lead
penetrates through the skin surface to an implanted distal
electrode.
[0047] The present invention also provides a novel process for
attenuating current flow through a lead wire for an active medical
device at a selected frequency, comprising the steps of: selecting
a capacitor which is resonant at the selected frequency; selecting
an inductor which is resonant at the selected frequency; using the
capacitor and the inductor to form a tank filter circuit; and
placing the tank filter circuit in series with the lead wire.
[0048] The overall Q of the tank filter circuit may be reduced by
increasing the Q of the inductor and reducing the Q of the
capacitor. In this regard, minimizing resistive loss in the
inductor maximizes the Q of the inductor, and raising the
equivalent series resistance of the capacitor minimizes the Q of
the capacitor.
[0049] The net effect is to reduce the overall Q of the tank filter
circuit which widens the band stop width to attenuate current flow
through the lead wire along a range of selected frequencies. As
discussed herein, the range of selected frequencies may include a
plurality of MRI pulse frequencies.
[0050] Other features and advantages of the present invention will
become apparent from the following more detailed description, taken
in conjunction with the accompanying drawings which illustrate, by
way of example, the principles of the invention.
BRIEF DESCRIPTION OF THE DRAWINGS
[0051] The accompanying drawings illustrate the invention. In such
drawings:
[0052] FIG. 1 is a wire-formed diagram of a generic human body
showing a number of active implantable medical devices (AIMDs);
[0053] FIG. 2 is a perspective and somewhat schematic view of a
prior art active implantable medical device (AIMD) including a lead
wire directed to the heart of a patient;
[0054] FIG. 3 is an enlarged sectional view taken generally along
the line 3-3 of FIG. 2;
[0055] FIG. 4 is a view taken generally along the line 4'4 of FIG.
3;
[0056] FIG. 5 is a perspective/isometric view of a prior art
rectangular quadpolar feedthrough capacitor of the type shown in
FIGS. 3 and 4;
[0057] FIG. 6 is sectional view taken generally along the line 6-6
of FIG. 5;
[0058] FIG. 7 is a sectional view taken generally along the line
7-7 of FIG. 5;
[0059] FIG. 8 is a diagram of a unipolar active implantable medical
device;
[0060] FIG. 9 is a diagram similar to FIG. 8, illustrating a
bipolar AIMD system;
[0061] FIG. 10 is a diagram similar to FIGS. 8 and 9, illustrating
a biopolar lead wire system with a distal TIP and RING, typically
used in a cardiac pacemaker;
[0062] FIG. 11 is a schematic diagram showing a parallel
combination of an inductor L and a capacitor C placed in series
with the lead wire systems of FIGS. 8-10;
[0063] FIG. 12 is a chart illustrating calculation of frequency of
resonance for the parallel tank circuit of FIG. 11;
[0064] FIG. 13 is a graph showing impedance versus frequency for
the parallel tank band stop circuit of FIG. 11;
[0065] FIG. 14 is an equation for the impedance of an inductor in
parallel with a capacitor;
[0066] FIG. 15 is a chart illustrating reactance equations for the
inductor and the capacitor of the parallel tank circuit of FIG.
11;
[0067] FIG. 16 is a schematic diagram illustrating the parallel
tank circuit of FIG. 1, except in this case the inductor and the
capacitor have series resistive losses;
[0068] FIG. 17 is a diagram similar to FIG. 8, illustrating the
tank circuit/band stop filter added near a distal electrode;
[0069] FIG. 18 is a schematic representation of the novel band stop
tank filter of the present invention, using switches to illustrate
its function at various frequencies;
[0070] FIG. 19 is a schematic diagram similar to FIG. 18,
illustrating the low frequency model of the band stop filter;
[0071] FIG. 20 is a schematic diagram similar to FIGS. 18 and 19,
illustrating the model of the band stop filter of the present
invention at its resonant frequency;
[0072] FIG. 21 is a schematic diagram similar to FIGS. 18-20,
illustrating a model of the band stop filter at high frequencies
well above the resonant frequency;
[0073] FIG. 22 is a decision tree block diagram illustrating a
process for designing the band stop filters of the present
invention;
[0074] FIG. 23 is graph of insertion loss versus frequency for band
stop filters having high Q inductors and differing quality "Q"
factors;
[0075] FIG. 24 is a tracing of an exemplary patient x-ray showing
an implanted pacemaker and cardioverter defibrillator and
corresponding lead wire system;
[0076] FIG. 25 is a line drawings of an exemplary patent cardiac
x-ray of a biventricular lead wire system;
[0077] FIG. 26 illustrates a bipolar cardiac pacemaker lead wire
showing the distal TIP and the distal RING electrodes; and
[0078] FIG. 27 is an enlarged, fragmented schematic illustration of
the area illustrated by the line 27-27 in FIG. 26.
DETAILED DESCRIPTION OF THE PREFERRED EMBODIMENT
[0079] FIG. 1 illustrates of various types of active implantable
and external medical devices 100 that are currently in use. FIG. 1
is a wire formed diagram of a generic human body showing a number
of implanted medical devices. 100A is a family of external and
implantable hearing devices which can include the group of hearing
aids, cochlear implants, piezoelectric sound bridge transducers and
the like. 100B includes an entire variety of neurostimulators and
brain stimulators. Neurostimulators are used to stimulate the Vagus
nerve, for example, to treat epilepsy, obesity and depression.
Brain stimulators are similar to a pacemaker-like device and
include electrodes implanted deep into the brain for sensing the
onset of the seizure and also providing electrical stimulation to
brain tissue to prevent the seizure from actually happening. The
lead wires that come from a deep brain stimulator are often placed
using real time imaging. Most commonly such lead wires are placed
during real time MRI. 100C shows a cardiac pacemaker which is
well-known in the art. 100D includes the family of left ventricular
assist devices (LVAD's), and artificial hearts, including the
recently introduced artificial heart known as the Abiocor. 100E
includes an entire family of drug pumps which can be used for
dispensing of insulin, chemotherapy drugs, pain medications and the
like insulin pumps are evolving from passive devices to ones that
have sensors and closed loop systems. That is, real time monitoring
of blood sugar levels will occur. These devices tend to be more
sensitive to EMI than passive pumps that have no sense circuitry or
externally implanted lead wires. 100F includes a variety of
external or implantable bone growth stimulators for rapid healing
of fractures. 100G includes urinary incontinence devices. 100H
includes the family of pain relief spinal cord stimulators and
anti-tremor stimulators. 100H also includes an entire family of
other types of neurostimulators used to block pain. 100I includes a
family of implantable cardioverter defibrillators (ICD) devices and
also includes the family of congestive heart failure devices (CHF).
This is also known in the art as cardio resynchronization therapy
devices, otherwise knows as CRT devices. 100J illustrates an
externally worn pack. This pack could be an external insulin pump,
an external drug pump, an external neurostimulator, a Holter
monitor with skin electrodes or even a ventricular assist device
power pack. 100K illustrates the insertion of an external probe or
catheter. These probes can be inserted into the femoral artery, for
example, or in any other number of locations in the human body.
[0080] Referring now to FIG. 2, a prior art active implantable
medical device (AIMD) 100 is illustrated. In general, the AIMD 100
could, for example, be a cardiac pacemaker 100C which is enclosed
by a titanium housing 102 as indicated. The titanium housing is
hermetically sealed, however there is a point where lead wires 104
must ingress and egress the hermetic seal. This is accomplished by
providing a hermetic terminal assembly 106. Hermetic terminal
assemblies are well known and generally consist of a ferrule 108
which is laser welded to the titanium housing 102 of the AIMD 100.
The hermetic terminal assembly 106 with its associated EMI filter
is better shown in FIG. 3. Referring once again to FIG. 2, four
lead wires are shown consisting of lead wire pair 104a and 104b and
lead wire pair 104c and 104d. This is typical of what's known as a
dual chamber bipolar cardiac pacemaker.
[0081] The ISI connectors 110 that are designed to plug into the
header block 112 are low voltage (pacemaker) connectors covered by
an ANSI/AAMI standard IS-1. Higher voltage devices, such as
implantable cardioverter defibrillators, are covered by a standard
known as the ANSI/AAMI DF-1. There is a new standard under
development which will integrate both high voltage and low voltage
connectors into a new miniature connector series known as the IS-4
series. These connectors are typically routed in a pacemaker
application down into the right ventricle and right atrium of the
heart 114. There are also new generation devices that have been
introduced to the market that couple lead wires to the outside of
the left ventricle. These are known as biventricular devices and
are very effective in cardiac resynchronization therapy (CRT) and
treating congestive heart failure (CHF).
[0082] Referring once again to FIG. 2, one can see, for example,
the bipolar lead wires 104a and 104b that could be routed, for
example, to the distal TIP and RING into the right ventricle. The
bipolar lead wires 104c and 104d could be routed to a distal TIP
and RING in the right atrium. There is also an RF telemetry pin
antenna 116 which is not connected to the IS-1 or DS-1 connector
block. This acts as a short stub antenna for picking up telemetry
signals that are transmitted from the outside of the device
100.
[0083] It should also be obvious to those skilled in the art that
all of the descriptions herein are equally applicable to other
types of AIMDs. These include implantable cardioverter
defibrillators (ICDs), neurostimulators, including deep brain
stimulators, spinal cord stimulators, cochlear implants,
incontinence stimulators and the like, and drug pumps. The present
invention is also applicable to a wide variety of minimally
invasive AIMDs. For example, in certain hospital cath lab
procedures, one can insert an AIMD for temporary use such as an
ICD. Ventricular assist devices also can fall into this type of
category. This list is not meant to be limiting, but is only
example of the applications of the novel technology currently
described herein.
[0084] FIG. 3 is an enlarged, fragmented cross-sectional view taken
generally along line 3-3 of FIG. 2. Here one can see in
cross-section the RF telemetry pin 116 and the bipolar lead wires
104a and 104c which would be routed to the cardiac chambers by
connecting these lead wires to the internal connectors 118 of the
IS-1 header block 112 (FIG. 2). These connectors are designed to
receive the plug 110 which allows the physicians to thread lead
wires through the venous system down into the appropriate chambers
of the heart 114. It will be obvious to those skilled in the art
that tunneling of deep brain electrodes or neurostimulators is
equivalent.
[0085] Referring back to FIG. 3, one can see a prior art
feedthrough capacitor 120 which has been bonded to the hermetic
terminal assembly 106. These feedthrough capacitors are well known
in the art and are described and illustrated in U.S. Pat. Nos.
5,333,095, 5,751,539, 5,978,204, 5,905,627, 5,959,829, 5,973,906,
5,978,204, 6,008,980, 6,159,560, 6,275,369, 6,424,234, 6,456,481,
6,473,291, 6,529,103, 6,566,978, 6,567,259, 6,643,903, 6,675,779,
6,765,780 and 6,882,248. In this case, a rectangular quadpolar
feedthrough capacitor 120 is illustrated which has an external
metalized termination surface 122. It includes embedded electrode
plate sets 124 and 126. Electrode plate set 124 is known as the
ground electrode plate set and is terminated at the outside of the
capacitor 120 at the termination surface 122. These ground
electrode plates 124 are electrically and mechanically connected to
the ferrule 108 of the hermetic terminal assembly 106 using a
thermosetting conductive polyimide or equivalent material 128
(equivalent materials will include solders, brazes, conductive
epoxies and the like). In turn, the hermetic seal terminal assembly
106 is designed to have its titanium ferrule 108 laser welded 130
to the overall housing 102 of the AIMD 100. This forms a continuous
hermetic seal thereby preventing body fluids from penetrating into
and causing damage to the electronics of the AIMD.
[0086] It is also essential that the lead wires 104 and insulator
136 be hermetically sealed, such as by the gold brazes or glass
seals 132 and 134. The gold braze 132 wets from the titanium
ferrule 108 to the alumina ceramic insulator 136. In turn, the
ceramic alumina insulator 136 is also gold brazed at 134 to each of
the lead wires 104. The RF telemetry pin 116 is also gold brazed at
138 to the alumina ceramic insulator 136. It will be obvious to
those skilled in the art that there are a variety of other ways of
making such a hermetic terminal. This would include glass sealing
the leads into the ferrule directly without the need for the gold
brazes.
[0087] As shown in FIG. 3, the RF telemetry pin 116 has not been
included in the area of the feedthrough capacitor 120. The reason
for this is the feedthrough capacitor 120 is a very broadband
single element EMI filter which would eliminate the desirable
telemetry frequency.
[0088] FIG. 4 is a bottom view taken generally along line 4-4 in
FIG. 3. One can see the gold braze 132 which completely seals the
hermetic terminal insulator 136 into the overall titanium ferrule
108. One can also see the overlap of the capacitor attachment
materials, shown as a thermosetting conductive adhesive 128, which
makes contact to the gold braze 132 that forms the hermetic
terminal 106.
[0089] FIG. 5 is an isometric view of the feedthrough capacitor
120. As one can see, the termination surface 122 connects to the
capacitor's internal ground plate set 124. This is best seen in
FIG. 6 where ground plate set 124, which is typically silk-screened
onto ceramic layers, is brought out and exposed to the termination
surface 122. The capacitor's four (quadpolar) active electrode
plate sets 126 are illustrated in FIG. 7. In FIG. 6 one can see
that the lead wires 104 are in non-electrical communication with
the ground electrode plate set 124. However, in FIG. 7 one can see
that each one of the lead wires 104 is in electrical contact with
its corresponding active electrode plate set 126. The amount of
capacitance is determined by the overlap of the active electrode
plate area 126 over the ground electrode plate area. One can
increase the amount of capacitance by increasing the area of the
active electrode plate set 126. One can also increase the
capacitance by adding additional layers. In this particular
application, we are only showing six electrode layers: three ground
plates 124 and three active electrode plate sets 126 (FIG. 3).
However, 10, 60 or even more than 100 such sets can be placed in
parallel thereby greatly increasing the capacitance value. The
capacitance value is also related to the dielectric thickness or
spacing between the ground electrode set 124 and the active
electrode set 126. Reducing the dielectric thickness increases the
capacitance significantly while at the same time reducing its
voltage rating. This gives the designer many degrees of freedom in
selecting the capacitance value.
[0090] In the following description, functionally equivalent
elements shown in various embodiments will often be referred to
utilizing the same reference number.
[0091] FIG. 8 is a general diagram of a unipolar active implantable
medical device system 100. FIG. 8 could also be representative of
an externally worn medical device such as a Holter monitor. In the
case of a Holter monitor, the distal electrode 140 would typically
be a scan or patch electrode. The housing 102 of the active
implantable medical device 100 is typically titanium, ceramic,
stainless steel or the like. Inside of the device housing are the
AIMD electronic circuits. Usually AIMDs include a battery, but that
is not always the case. For example, for a Bion, it can receive its
energy from an external pulsing magnetic field. A lead wire 104 is
routed from the AIMD 100 to a point 140 where it is embedded in or
affixed to body tissue. In the case of a spinal cord stimulator
100H, the distal TIP 140 could be in the spinal cord. In the case
of a deep brain stimulator 100B, the distal electrode 140 would be
placed deep into the brain, etc. In the case of a cardiac pacemaker
100C, the distal electrode 140 would typically be placed in the
cardiac right ventricle.
[0092] FIG. 9 is very similar to FIG. 8 except that it is a bipolar
system. In this case, the electric circuit return path is between
the two distal electrodes 140 and 140. In the case of a cardiac
pacemaker 100C, this would be known as a bipolar lead wire system
with one of the electrodes known as the distal TIP 142 and the
other electrode which would float in the blood pool known as the
RING 144 (see FIG. 10). In contrast, the electrical return path in
FIG. 8 is between the distal electrode 140 through body tissue to
the conductive housing 102 of the implantable medical device
100.
[0093] FIG. 10 illustrates a bipolar lead wire system with a distal
TIP 142 and RING 144 typically as used in a cardiac pacemaker 100C.
In all of these applications, the patient could be exposed to the
fields of an MRI scanner or other powerful emitter used during a
medical diagnostic procedure. Currents that are directly induced in
the lead wire system 104 can cause heating by I.sup.2R losses in
the lead wire system or by heating caused by current flowing in
body tissue. If these currents become excessive, the associated
heating can cause damage or even destructive ablation to body
tissue.
[0094] The distal TIP 142 is designed to be implanted into or
affixed to the actual myocardial tissue of the heart. The RING 144
is designed to float in the blood pool. Because the blood is
flowing and is thermally conductive, the RING 144 structure is
substantially cooled. In theory, however, if the lead curves, the
RING 144 could also touch and become encapsulated by body tissue.
The distal TIP 142, on the other hand, is always thermally
insulated by surrounding body tissue and can readily heat up due to
the RF pulse currents of an MRI field.
[0095] FIG. 11 is a schematic diagram showing a parallel
combination of an inductor L and a capacitor C to be placed in the
lead wire systems 104 previously described. This combination forms
a parallel tank circuit or band stop filter 146 which will resonate
at a particular frequency (f.sub.r).
[0096] FIG. 12 gives the frequency of resonance equation f.sub.r
for the parallel tank circuit 146 of FIG. 11: where f.sub.r is the
frequency of resonance in hertz, L is the inductance in henries and
C is the capacitance in farads. MRI systems vary in static field
strength from 0.5 Tesla all the way up to 3 Tesla with newer
research machines going much higher. This is the force of the main
static magnetic field. The frequency of the pulsed RF field
associated with MRI is found by multiplying the static field in
Teslas times 42.45. Accordingly, a 3 Tesla MRI system has a pulsed
RF field of approximately 128 MHz.
[0097] Referring once again to FIG. 11, one can see that if the
values of the inductor and the capacitor are selected properly, one
could obtain a parallel tank resonant frequency of 128 MHz. For a
1.5 Tesla MRI system, the RF pulse frequency is 64 MHz. Referring
to FIG. 12, one can see the calculations assuming that the inductor
value L is equal to one nanohenry. The one nanohenry comes from the
fact that given the small geometries involved inside of the human
body, a very large inductor will not be possible. This is in
addition to the fact that the use of ferrite materials or iron
cores for such an inductor are not practical for two reasons: 1)
the static magnetic field from the MRI scanner would align the
magnetic dipoles (saturate) in such a ferrite and therefore make
the inductor ineffective; and 2) the presence of ferrite materials
will cause severe MRI image artifacts. What this means is that if
one were imaging the right ventricle of the heart, for example, a
fairly large area of the image would be blacked out or image
distorted due to the presence of these ferrite materials and the
way it interacts with the MRI field. It is also important that the
inductance value not vary while in the presence of the main static
field.
[0098] The relationship between the parallel inductor L and
capacitor C is also very important. One could use, for example, a
very large value of inductance which would result in a very small
value of capacitance to be resonant, for example, at the MRI
frequency of 64 MHz. However, using a very high value of inductor
results in a high number of turns of very small wire. Using a high
number of turns of very small diameter wire is contraindicated for
two reasons. The first reason is that the long length of relatively
small diameter wire results in a very high DC resistance for the
inductor. This resistance is very undesirable because low frequency
pacing or neurostimulator pulses would lose energy passing through
the relatively high series resistance. This is also undesirable
where the AIMD is sensing biologic signals. For example, in the
case of a pacemaker or deep brain stimulator, continuous sensing of
low frequency biological signals is required. Too much series
resistance in a lead wire system will attenuate such signals
thereby making the AIMD less efficient. Accordingly, it is a
preferred feature of the present invention that a relatively large
value of capacitance will be used in parallel with a relatively
small value of inductance, for example, employing highly
volumetrically efficient ceramic dielectric capacitors that can
create a great deal of capacitance in a very small space.
[0099] It should be also noted that below resonance, particularly
at very low frequencies, the current in the parallel L-C band width
stop filter passes through the inductor element. Accordingly, it is
important that the parasitic resistance of the inductor element be
quite low. Conversely, at very low frequencies, no current passes
through the capacitor element. At high frequencies, the reactance
of the capacitor element drops to a very low value. However, as
there is no case where it is actually desirable to have high
frequencies pass through the tank filter, the parasitic resistive
loss of the capacitor is not particularly important. This is also
known as the capacitor's equivalent series resistance (ESR). A
component of capacitor ESR is the dissipation factor of the
capacitor (a low frequency phenomena). Off of resonance, it is not
particularly important how high the capacitor's dissipation factor
or overall ESR is when used as a component of a parallel tank
circuit 116 as described herein. Accordingly, an air wound inductor
is the ideal choice because it is not affected by MRI signals or
fields. Because of the space limitations, however, the inductor
will not be very volumetrically efficient. For this reason, it is
preferable to keep the inductance value relatively low (in the
order of 1 to 100 nanohenries).
[0100] Referring once again to FIG. 12, one can see the
calculations for capacitance by algebraically solving the resonant
frequency f.sub.r equation shown for C. Assuming an inductance
value of one nanohenry, one can see that 6 nano-farads of
capacitance would be required. Six nano-farads of capacitance is a
relatively high value of capacitance. However, ceramic dielectrics
that provide a very high dielectric constant are well known in the
art and are very volumetrically efficient. They can also be made of
biocompatible materials making them an ideal choice for use in the
present invention.
[0101] FIG. 13 is a graph showing impedance versus frequency for
the parallel tank, band stop filter circuit 146 of FIG. 11. As one
can see, using ideal circuit components, the impedance measured
between points A and B for the parallel tank circuit 146 shown in
FIG. 11 is very low (zero) until one approaches the resonant
frequency f.sub.r At the frequency of resonance, these ideal
components combine together to look like a very high or, ideally,
an infinite impedance. The reason for this comes from the
denominator of the equation Z.sub.ab for the impedance for the
inductor in parallel with the capacitor shown as FIG. 14. When the
inductive reactance is equal to the capacitive reactance, the two
imaginary vectors cancel each other and go to zero. Referring to
the equations in FIGS. 14 and 15, one can see in the impedance
equation for Z.sub.ab, that a zero will appear in the denominator
when X.sub.L=X.sub.C. This has the effect of making the impedance
approach infinity as the denominator approaches zero. As a
practical matter, one does not really achieve an infinite
impedance. However, tests have shown that several hundred ohms can
be realized which offers a great deal of attenuation and protection
to RF pulsed currents from MRI. What this means is that at one
particular unique frequency, the impedance between points A and B
in FIG. 11 will appear very high (analogous to opening a switch).
Accordingly, it would be possible, for example, in the case of a
cardiac pacemaker, to design the cardiac pacemaker for
compatibility with one single popular MRI system. For example, in
the AIMD patient literature and physician manual it could be noted
that the pacemaker lead wire system has been designed to be
compatible with 3 Tesla MRI systems. Accordingly, with this
particular device, a distal TIP band stop filter 146 would be
incorporated where the L and the C values have been carefully
selected to be resonant at 128 MHz, presenting a high or almost
infinite impedance at the MRI pulse frequency.
[0102] FIG. 16 is a schematic drawing of the parallel tank circuit
146 of FIG. 11, except in this case the inductor L and the
capacitor C are not ideal. That is, the capacitor C has its own
internal resistance R.sub.C, which is otherwise known in the
industry as dissipation factor or equivalent series resistance
(ESR). The inductor L also has a resistance R.sub.L. For those that
are experienced in passive components, one would realize that the
inductor L would also have some parallel capacitance. This
parasitic capacitance comes from the capacitance associated with
adjacent turns. However, the inductance value contemplated is so
low that one can assume that at MRI pulse frequencies, the
inductor's parallel capacitance is negligible. One could also state
that the capacitor C also has some internal inductance which would
appear in series. However, the novel capacitors described below are
very small or coaxial and have negligible series inductance.
Accordingly, the circuit shown in FIG. 16 is a very good
approximation model for the novel parallel tank circuits 146 as
described herein.
[0103] This is best understood by looking at the FIG. 16 circuit
146 at the frequency extremes. At very low frequency, the inductor
reactance equation is X.sub.L=2nfL (reference FIG. 15). When the
frequency f is close to zero (DC), this means that the inductor
looks like a short circuit. It is generally the case that biologic
signals are low frequency, typically between 10 Hz and 1000 Hz. For
example, in a cardiac pacemaker 1000, all of the frequencies of
interest appear between 10 Hz and 1000 Hz. At these low
frequencies, the inductive reactance X.sub.L will be very close to
zero ohms. Over this range, on the other hand, the capacitive
reactance X which has the equation X.sub.C=1/(2nfc) will look like
an infinite or open circuit (reference FIG. 15). As such, at low
frequencies, the impedance between points A and B in FIG. 16 will
equal to R.sub.L. Accordingly, the resistance of the inductor
(R.sub.L) should be kept as small as possible to minimize
attenuation of biologic signals or attenuation of stimulation
pulses to body tissues. This will allow biologic signals to pass
through the band stop filter 146 freely. It also indicates that the
amount of capacitive loss R.sub.C is not particularly important. As
a matter of fact, it would be desirable if that loss were fairly
high so as to not freely pass very high frequency signals (such as
undesirable EMI from cellular phones). It is also desirable to have
the Q of the circuit shown in FIG. 16 relatively low so that the
band stop frequency bandwidth can be a little wider. In other
words, in a preferred embodiment, it would be possible to have a
band stop wide enough to block both 64 MHz and 128 MHz frequencies
thereby making the medical device compatible for use in both 1.5
Tesla and 3 Tesla MRI systems.
[0104] FIG. 17 is a drawing of the unipolar AIMD lead wire system,
previously shown in FIG. 8, with the band stop filter 146 of the
present invention added near the distal electrode 140. As
previously described, the presence of the tank circuit 146 will
present a very high impedance at one or more specific MRI RF pulse
frequencies. This will prevent currents from circulating through
the distal electrode 140 into body tissue at this selected
frequency(s). This will provide a very high degree of important
protection to the patient so that overheating does not cause tissue
damage.
[0105] FIG. 18 is a representation of the novel band stop tank
filter 146 using switches that open and close at various
frequencies to illustrate its function. Inductor L has been
replaced with a switch S. When the impedance of the inductor is
quite low, the switch S.sub.L will be closed. When the impedance or
inductive reactance of the inductor is high, the switch S.sub.L
will be shown open. There is a corresponding analogy for the
capacitor element C. When the capacitive reactance looks like a
very low impedance, the capacitor switch S.sub.C will be shown
closed. When the capacitive reactance is shown as a very high
impedance, the switch S.sub.C will be shown open. This analogy is
best understood by referring to FIGS. 19, 20 and 21.
[0106] FIG. 19 is the low frequency model of the band stop filter
146. At low frequencies, capacitors tend to look like open circuits
and inductors tend to look like short circuits. Accordingly, switch
S.sub.L is closed and switch S.sub.C is open. This is an indication
that at frequencies below the resonant frequency of the band stop
filter 146 that currents will flow only through the inductor
element and its corresponding resistance R.sub.L. This is an
important consideration for the present invention that low
frequency biological signals not be attenuated. For example, in a
cardiac pacemaker, frequencies of interest generally fall between
10 Hz and 1000 Hz. Pacemaker pacing pulses fall within this general
frequency range. In addition, the implantable medical device is
also sensing biological frequencies in the same frequency range.
Accordingly, such signals must be able to flow readily through the
band stop filter's inductor element. A great deal of attention
should be paid to the inductor design so that it has a very high
quality factor (Q) and a very low value of parasitic series
resistance R.sub.L.
[0107] FIG. 20 is a model of the novel band stop filter 146 at its
resonant frequency. By definition, when a parallel tank circuit is
at resonance, it presents a very high impedance to the overall
circuit. Accordingly, both switches S.sub.L and S.sub.C are shown
open. For example, this is how the band stop filter 146 prevents
the flow of MRI currents through pacemaker lead wires and/or into
body tissue at a selected MRI RF pulsed frequency.
[0108] FIG. 21 is a model of the band stop filter 146 at high
frequency. At high frequencies, inductors tend to look like open
circuits. Accordingly, switch S.sub.L is shown open. At high
frequencies, ideal capacitors tend to look like short circuits,
hence switch S.sub.C is closed. It should be noted that real
capacitors are not ideal and tend to degrade in performance at high
frequency. This is due to the capacitor's equivalent series
inductance and equivalent series resistance. Fortunately, for the
present invention, it is not important how lossy (resistive) the
capacitor element C gets at high frequency. This will only serve to
attenuate unwanted electromagnetic interference from flowing in the
lead wire system. Accordingly, in terms of biological signals, the
equivalent series resistance R.sub.C and resulting quality factor
of the capacitor element C is not nearly as important as the
quality factor of the inductor element L. The equation for
inductive reactance (X.sub.L) is given in FIG. 15. The capacitor
reactance equation. (X.sub.C) is also given in FIG. 15. As one can
see, when one inserts zero or infinity for the frequency, one
derives the fact that at very low frequencies inductors tend to
look like short circuits and capacitors tend to look like open
circuits. By inserting a very high frequency into the same
equations, one can see that at very high frequency ideal inductors
look like an infinite or open impedance and ideal capacitors look
like a very low or short circuit impedance.
[0109] FIG. 22 is a decision, tree block diagram that better
illustrates the design process herein. Block 148 is an initial
decision step the designer must make. For illustrative purposes, we
will start with a value of capacitance that is convenient. This
value of capacitance is generally going to relate to the amount of
space available in the AIMD lead wire system and other factors.
These values for practical purposes generally range in capacitance
value from a few tens of picofarads up to about 10,000 picofarads.
This puts practical boundaries on the amount of capacitance that
can be effectively packaged within the scope of the present
invention. However, that is not intended to limit the general
principles of the present invention, but just describe a preferred
embodiment. Accordingly, in the preferred embodiment, one will
select capacitance values generally ranging from 100 picofarads up
to about 4000 picofarads and then solve for a corresponding
inductance value required to be self-resonant at the selected
telemetry frequency. Referring back to FIG. 22, one makes the
decision whether the design was C first or L first. If one makes a
decision to assume a capacitance value C first then one is directed
to the left to block 150. In block 150, one does an assessment of
the overall packaging requirements of a distal TIP 142 band stop
filter 146 and then assumes a realizable capacitance value. So, in
decision block 150, we assume a capacitor value. We then solve the
resonant tank equation f.sub.r from FIG. 12 at block 152 for the
required value of inductance (L). We then look at a number of
inductor designs to see if the inductance value is realizable
within the space, parasitic resistance R.sub.C, and other
constraints of the design. If the inductance value is realizable,
then we go on to block 154 and finalize the design. If the
inductance value is not realizable within the physical and
practical constraints, then we need to go back to block 150 and
assume a new value of capacitance. One may go around this loop a
number of times until one finally comes up with a compatible
capacitor and an inductor design. In some cases, one will not be
able to achieve a final design using this alone. In other words,
one may have to use a custom capacitor value or design in order to
achieve a result that meets all of the design criteria. That is, a
capacitor design with high enough internal losses R.sub.C and an
inductor design with low internal loss R.sub.L such that the band
stop filter 146 has the required quality factor (Q), that it be
small enough in size, that it have sufficient current and high
voltage handling capabilities and the like. In other words, one has
to consider all of the design criteria in going through this
decision tree.
[0110] In the case where one has gone through the left hand
decision tree consisting of blocks 150, 152 and 154 a number of
times and keeps coming up with a "no," then one has to assume a
realizable value of inductance and go to the right hand decision
tree starting at block 156. One then assumes a realizable value of
inductance (L) with a low enough series resistance for the inductor
R.sub.L such that it will work and fit into the design space and
guidelines. After one assumes that value of inductance, one then
goes to decision block 158 and solves the equation C in FIG. 12 for
the required amount of capacitance. After one finds the desired
amount of capacitance C, one then determines whether that custom
value of capacitance will fit into the design parameters. If the
capacitance value that is determined in step 160 is realizable,
then one goes on and finalizes the design. However, if it is not
realizable, then one can go back up to step 156, assume a different
value of L and go through the decision tree again. This is done
over and over until one finds combinations of L and C that are
practical for the overall design.
[0111] For purposes of the present invention, it is possible to use
series discrete inductors or parallel discrete capacitors to
achieve the same overall result. For example, in the case of the
inductor element L, it would be possible to use two, three or even
more (n) individual inductor elements in series. The same is true
for the capacitor element that appears in the parallel tank filter
146. By adding or subtracting capacitors in parallel, we are also
able to adjust the total capacitance that ends up resonating in
parallel with the inductance.
[0112] It is also possible to use a single inductive component that
has significant parasitic capacitance between its adjacent turns. A
careful designer using multiple turns could create enough parasitic
capacitance such that the coil becomes self-resonant at a
predetermined frequency. In this case, the predetermined frequency
would be the MRI pulsed frequency.
[0113] Efficiency of the overall tank circuit 146 is also measured
in terms of a quality factor, Q, although this factor is defined
differently than the one previously mentioned for discrete
capacitors and inductors. The circuit Q is typically expressed
using the following equation:
Q=f.sub.r/.DELTA.f.sub.3dB
Where f.sub.r is the resonance frequency, and .DELTA.f.sub.3dB
shown as points a and b in FIG. 23, is the bandwidth of the band
stop filter 146. Bandwidth is typically taken as the difference
between the two measured frequencies, f.sub.1 and f.sub.2, at the 3
dB loss points as measured on an insertion loss chart, and the
resonance frequency is the average between f.sub.1 and f.sub.2. As
can be seen in this relationship, higher Q values result in a
narrower 3 dB bandwidth.
[0114] Material and application parameters must be taken into
consideration when designing tank filters. Most capacitor
dielectric materials age 1%-5% in capacitance values per decade of
time elapsed, which can result in a shift of the resonance
frequency of upwards of 2.5%. In a high-Q filter, this could result
in a significant and detrimental drop in the band stop filter
performance. A lower-Q filter would minimize the effects of
resonance shift and would allow a wider frequency band through the
filter. However, very low Q filters display lower than desirable
attenuation behavior at the desired band stop frequency (see FIG.
23, curve 162). For this reason, the optimum Q for the band stop
filter of the present invention will embody a high Q inductor L and
a relatively low Q capacitor C which will result in a medium Q tank
filter as shown in curve 164 of FIG. 23.
[0115] Accordingly, the "Q" or quality factor of the tank circuit
is very important. As mentioned, it is desirable to have a very low
loss circuit at low frequencies such that the biological signals
not be undesirably attenuated. The quality factor not only
determines the loss of the filter, but also affects its 3 dB
bandwidth. If one does a plot of the filter response curve (Bode
plot), the 3 dB bandwidth determines how sharply the filter will
rise and fall. With reference to curve 166 of FIG. 23, for a tank
that is resonant at 128 MHz, an ideal response would be one that
had infinite attenuation at 128 MHz, but had zero attenuation at
low frequencies below 1 KHz. Obviously, this is not possible given
the space limitations and the realities of the parasitic losses
within components. In other words, it is not possible (other than
at cryogenic temperatures) to build an inductor that has zero
internal resistance. On the other hand, it is not possible to build
a perfect (ideal) capacitor either. Capacitors have internal
resistance known as equivalent series resistance and also have
small amounts of inductance. Accordingly, the practical realization
of a circuit, to accomplish the purposes of the present invention,
is a challenging one.
[0116] The performance of the circuit is directly related to the
efficiency of both the inductor and the capacitor; the less
efficient each component is, the more heat loss that results, and
this can be expressed by the addition of resistor elements to the
ideal circuit diagram. The effect of lower Q in the tank circuit is
to broaden the resonance peak about the resonance frequency. By
deliberately using a low Q capacitor, one can broaden the resonance
such that a high impedance (high attenuation) is presented at
multiple MRI RF frequencies, for example 64 MHz and 128 MHz.
[0117] Referring again to FIG. 23, one can see curve 164 wherein a
low resistive loss high Q inductor has been used in combination
with a relatively high ESR low Q capacitor. This has a very
desirable effect in that at very low frequencies, the impedance of
the tank circuit 146 is essentially zero ohms (or zero dB loss).
This means that biologic frequencies are not undesirably
attenuated. However, one can see that the 3 db bandwidth is much
larger. This is desirable as it will block multiple RF frequencies.
As one goes even higher in frequency, curve 164 will desirably
attenuate other high frequency EMI signals, such as those from
cellular telephones, microwave ovens and the like. Accordingly, it
is often desirable that very low loss inductors be used in
combination with relatively high loss (and/or high inductance)
capacitors to achieve a medium or lower Q band stop filter. Again
referring to FIG. 23, one can see that if the Q of the overall
circuit or of the individual components becomes too low, then we
have a serious degradation in the overall attenuation of the band
stop filter at the MRI pulse frequencies. Accordingly, a careful
balance between component design and tank circuit Q must be
achieved.
[0118] Referring once again to FIG. 17, one can also increase the
value of R.sub.C by adding a separate discrete component in series
with the capacitor element. For example, one could install a small
capacitor chip that had a very low equivalent series resistance and
place it in series with a resistor chip. This would be done to
deliberately raise the value of R.sub.C in the circuit as shown in
FIG. 17. By carefully adjusting this value of R.sub.C, one could
then achieve the ideal curve 164 as shown in FIG. 23.
[0119] FIG. 24 is a tracing of an actual patient X-ray. This
particular patient required both a cardiac pacemaker 1000 and an
implantable cardioverter defibrillator 1001. The corresponding lead
wire system 104, as one can see, makes for a very complicated
antenna and loop coupling situation. The reader is referred to the
article entitled, "Estimation of Effective Lead Loop Area for
Implantable Pulse Generator and Implantable Cardioverter
Defibrillators" provided by the AAMI Pacemaker EMC Task Force.
[0120] Referring again to FIG. 24, one can see that from the
pacemaker 1000, there is an electrode in both the right atrium and
in the right ventricle. Both these involve a TIP and RING
electrode. In the industry, this is known as a dual chamber bipolar
lead wire system. Accordingly, the band stop filters 146 of the
present invention would need to be placed at least in the distal
TIP in the right atrium and the distal TIP in the right ventricle
from the cardiac pacemaker. One can also see that the implantable
cardioverter defibrillator (ICD) 100I is implanted directly into
the right ventricle. Its shocking TIP and perhaps its super vena
cava (SVC) shock coil would also require a band stop filters of the
present invention so that MRI exposure cannot induce excessive
currents into the associated lead wire system (S). Modern
implantable cardioverter defibrillators (ICDs) incorporate both
pacing and cardioverting (shock) features. Accordingly, it is
becoming quite rare for a patient to have a lead wire layout as
shown in the X-ray of FIG. 24. However, the number of electrodes
remain the same. There are also newer combined pacemaker/ICD
systems which include biventricular pacemaking (pacing of the left
ventricle). These systems can have as many as 9 to even 12 lead
wires.
[0121] FIG. 25 is a line drawing of an actual patient cardiac X-ray
of one of the newer bi-ventricular lead wire systems with various
types of electrode TIPS shown. The new hi-ventricular systems are
being used to treat congestive heart failure, and make it possible
to implant leads outside of the left ventricle. This makes for a
very efficient pacing system; however, the lead wire system 104 is
quite complex. When a lead wire system 104, such as those described
in FIGS. 8, 9, 10 and 11, are exposed to a time varying
electromagnetic field, electric currents can be induced into such
lead wire systems. For the hi-ventricular system, band stop filters
146 would be required at each of the three distal TIPs and
optionally at RING and SVC locations.
[0122] FIG. 26 illustrates a single chamber bipolar cardiac
pacemaker lead wire showing the distal TIP 142 and the distal RING
144 electrodes. This is a spiral wound system where the RING coil
104 is wrapped around the TIP coil 104'. There are other types of
pacemaker lead wire systems in which these two leads lay parallel
to one another (known as a bifilar lead system).
[0123] FIG. 27 is a schematic illustration of the area 27-27 in
FIG. 26. In the area of the distal TIP 142 and RING 144 electrodes,
band stop filters 146 and 146 have been placed in series with each
of the respective TIP and RING circuits. Accordingly, at MRI pulsed
frequencies, an open circuit will be presented thereby stopping the
flow of undesirable RF current.
[0124] Although several embodiments of the invention have been
described in detail, for purposes of illustration, various
modifications of each may be made without departing from the spirit
and scope of the invention. Accordingly, the invention is not to be
limited, except as by the appended claims.
* * * * *