U.S. patent number 3,837,930 [Application Number 05/325,313] was granted by the patent office on 1974-09-24 for method of producing iron-chromium-aluminum alloys with improved high temperature properties.
This patent grant is currently assigned to The International Nickel Company, Inc.. Invention is credited to John Stanwood Benjamin, Robert Lacock Cairns.
United States Patent |
3,837,930 |
Cairns , et al. |
September 24, 1974 |
METHOD OF PRODUCING IRON-CHROMIUM-ALUMINUM ALLOYS WITH IMPROVED
HIGH TEMPERATURE PROPERTIES
Abstract
A powder metallurgy product comprising iron and chromium, and/or
aluminum and characterized by elongated grains that are stable at
elevated temperatures. A method of producing such a product,
including mechanically alloying a suitable powder charge,
consolidating the mechanically alloyed powder, working the
consolidated product so as to achieve therein a reduction of at
least about 10 percent; and, then, heating the worked product to
produce coarse elongated grains therein. The product produced
according to the present invention exhibits good oxidation
resistance and good room temperature and elevated temperature
strength and ductility.
Inventors: |
Cairns; Robert Lacock (Suffern,
NY), Benjamin; John Stanwood (Suffern, NY) |
Assignee: |
The International Nickel Company,
Inc. (New York, NY)
|
Family
ID: |
22814974 |
Appl.
No.: |
05/325,313 |
Filed: |
January 22, 1973 |
Related U.S. Patent Documents
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Application
Number |
Filing Date |
Patent Number |
Issue Date |
|
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218404 |
Jan 17, 1972 |
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Current U.S.
Class: |
419/13; 419/14;
419/19; 419/32 |
Current CPC
Class: |
B22F
3/24 (20130101); C22C 33/02 (20130101); C22C
32/0026 (20130101); B22F 2998/10 (20130101); B22F
2003/248 (20130101); B22F 2003/208 (20130101); B22F
2009/041 (20130101); B22F 2998/10 (20130101); B22F
9/04 (20130101); B22F 3/1208 (20130101); B22F
3/20 (20130101) |
Current International
Class: |
C22C
32/00 (20060101); B22F 3/24 (20060101); B22f
003/18 (); C21d 007/19 () |
Field of
Search: |
;148/11.5F
;29/182.5 |
References Cited
[Referenced By]
U.S. Patent Documents
Other References
Wukusick et al.; "An Iron-Chromium-Aluminum Alloy Containing
Yttrium;" Materials Research & Standards; 12/1964, pp. 637-646.
.
Oda et al.; "Dispersion-Strengthened Ferritic Heat-Resisting
Steel;" Modern Developments in Powder Metallurgy; H. H. Hausner,
Ed.; Plenum Press, N.Y.; 1971, Vol. 5; pp. 159-168..
|
Primary Examiner: Stallard; W. W.
Parent Case Text
This application is a continuation-in-part of U.S. Application Ser.
No. 218,404, filed Jan. 17, 1972, and now abandoned.
Claims
We claim:
1. A method of producing a powder metallurgy product
comprising:
a. hot consolidating a mechanically alloyed powder produced by
mechanically alloying a powder mixture consisting essentially of,
by weight, at least one element from the group consisting of about
10 percent to about 40 percent chromium and about 1 percent to
about 10 percent aluminum, up to about 10 percent nickel, up to
about 20 percent cobalt, up to about 2 percent each of rare earth
metal, yttrium, zirconium, columbium, hafnium, tantalum, silicon,
and/or vanadium, up to about 6 percent each of tungsten and
molybdenum, and the balance iron, further comprising up to about 10
volume percent dispersoid material having a melting point of at
least 2750.degree.F., and
b. working the consolidated product at a temperature not higher
than the temperature range of about 1600.degree.F. to about
1700.degree.F. to achieve therein a reduction of at least about 10
percent, such that the resulting worked material will undergo grain
coarsening when subjected to an elevated grain coarsening
temperature.
2. The method defined in claim 1, wherein said reduction is at
least about 15 percent.
3. The method defined in claim 1, wherein said reduction is at
least about 25 percent.
4. The method defined in claim 1, wherein said mechanical alloying
is conducted in an inert atmosphere.
5. The method defined in claim 4, wherein said atmosphere consists
essentially of argon.
Description
Conventionally-produced iron-base alloys containing chromium and
aluminum exhibit oxidation resistance of a high order, even at
elevated temperatures, but are of limited practical utility because
they exhibit relatively low high-temperature strength, and are
generally subject to extreme grain coarsening and grain boundary
embrittlement when exposed for extended times to elevated
temperatures. Such alloys exhibit negligible room temperature
ductility after exposure to high temperature for extended periods
of time. As a result of these drawbacks, the use of such alloys has
largely been restricted to high-temperature applications at which
little strength is required, e.g., electrical resistance heating
elements, and to lower temperature applications where corrosion
conditions preclude the use of other materials. It is, therefore,
desirable to overcome the above-mentioned drawbacks so that such
alloys can be used in various other high temperature applications
requiring strength and corrosion resistance, such as turbines
vanes, burner cans and blades.
It appeared that the problem of drastic loss of ductility in such
iron-base alloys upon long-time exposure of the materials to
elevated temperature could be solved if the massive grain growth
found to occur therein during such elevated temperature exposure
could be prevented.
The mechanical alloying process described in U.S. Pat. No.
3,591,362 to Benjamin, provides a method of uniformly distributing
dispersoid particles at close spacings in such alloys.
Briefly, in the mechanical alloying process, as described in the
above patent, the constituent metal particles of the starting
powder charge are integrated together into dense composite
particles without melting any of the constituents, this being done
by dry milling the powder, usually in the presence of grinding
media, e.g., balls, so as to apply to the powder charge, mechanical
energy in the form of a plurality of repeatedly-applied high
energy, compressive forces. Such high energy forces result in the
fracture, or comminution, of the original powder constituents and
the welding together of the fragments so produced, as well as the
repeated fracture and re-welding of the welded fragments, so that
there is brought about a substantially complete codissemination of
the fragments of the various constituents of the starting powder.
The mechanically alloyed composite powder particles produced in
this manner are characterized metallographically by cohesive
internal structures in which the constituents are intimately united
to provide an interdispersion of comminuted fragments of the
starting constituents. Very short distances across the areas
corresponding to the fragments of initial materials in the
composite particles can be created, e.g., on the order of 3 microns
or 1 micron or less, and fine dispersoid particles present in the
powder charge can be uniformly distributed throughout the composite
particles at short interparticle spacings, e.g., one micron or
less.
The mechanical alloying process may be conducted in a variety of
equipment, including a stirred ball mill, shaker mill, vibratory
ball mill, planetary ball mill, and even certain ball mills
provided attention is had to the ball-to-powder ratio of the charge
and size of the mill, as taught by the above Benjamin patent.
It has been found particularly advantageous in obtaining optimum
results to employ agitation milling under high energy conditions in
which a substantial portion of the mass of the attritive elements,
e.g., balls, is maintained kinetically in a highly activated state
of relative motion. The milling is sufficiently energetic to reduce
substantially the thickness of the initial metal constituents by
impact compression resulting from collisions with the milling
medium, e.g., grinding balls. It has been found advantageous that
at least about 40 percent, e.g., 50 or 70 percent or even 90
percent or more, of the attritive elements be maintained in a
highly activated state.
By maintaining the attritive elements in a highly activated state
of mutual collision in a substantially dry environment and
throughout substantially the whole mass, optimum conditions are
provided for comminuting and cold welding the constituents,
accompanied by particle growth, to produce within each composite
particle, a mechanically alloyed structure of the constituents. The
resulting composite metal powder will be heavily cold worked and
will reach a high hardness level, which becomes substantially
constant ("saturation hardness") after a minimum milling time due
to impact compression of the particles arising from repeated
collision of the attractive elements upon the metal particles, such
hardness level providing stored energy to the composite powder
particles.
In the interest of providing composite particles of substantially
uniform composition and structure, milling is usually conducted
beyond the point at which saturation hardness is reached.
We have now discovered a powder metallurgy process for producing
iron-base alloys containing chromium and/or aluminum, which is
based upon the use of mechanically alloyed powders and which
provides alloys having markedly improved properties over a range of
temperatures up to at least about 2000.degree.F. We have also
discovered processing cycles which provide such alloys with a
stable, elongated grain structure having improved strength at
elevated temperatures and having good ductility over a wide range
of temperatures, permitting the provision of mill products,
including sheet, plate, wire, rod, tubing, etc., of greatly
enhanced utility as compared to such articles produced by
conventional means. Such grains provide to the consolidated
products significant improvement in the tensile and stress-rupture
strengths and ductility at elevated temperatures.
It is therefore an object of this invention to provide an iron base
material having improved high temperature strength.
It is a further object to provide such an iron base material that
exhibits good room temperature ductility even after extended
exposure to high temperature.
It is still another object to provide an iron base material that
exhibits grain-stability at elevated temperatures.
These and other objects will become more apparent when taken in
conjunction with the following description and the accompanying
figures, wherein:
FIG. 1 is a photomicrograph taken at 50 diameters of an iron-base
product made according to the present invention, which product was
cold-rolled 50 percent and grain coarsened by heating at
2,400.degree.F. for one hour.
FIG. 2 is a photomicrograph taken at 100 diameters of a wire
produced according to the present invention which wire was exposed
to a temperature of 2400.degree.F. for 160 hours.
Generally speaking, the present invention includes the mechanical
alloying of powder charges containing by weight, about 10 percent
to about 40 percent chromium; up to about 10 percent aluminum,
e.g., about 1 percent to about 10 percent aluminum; up to about 20
percent cobalt; up to about 10 percent nickel; up to about 5
percent titanium; up to about 2 percent each of rare earth metal,
yttrium, zirconium, columbium, hafnium, tantalum, silicon, and/or
vanadium; up to about 6 percent each of tungsten and molybdenum;
and the balance essentially iron, and further including by volume,
up to about 10 percent finely divided dispersoid material
consisting of oxides, nitrides, carbides, borides and other
refractory materials, which dispersoid material has a melting point
of at least about 2750.degree.F.; hot consolidating the
mechanically alloyed powder to a substantially completely dense
body (e.g., about 98 percent theoretical density or more); working
the consolidated body at a temperature within the range up to about
1600.degree.F. to 1700.degree.F. to achieve a reduction of about 10
to 15 percent or more therein; and then heating the worked body to
an elevated grain-growth temperature to produce coarse grains
elongated in the direction or directions of working and to provide
improved stress-rupture properties therein.
More preferably, the powder charge and consolidated material
produced therefrom contain, by weight about 15 to 40 percent
chromium, and even more preferably, about 18 percent to about 26
percent chromium; up to about 5 percent cobalt; up to about 6
percent nickel; about 1 percent to about 7 percent aluminum, e.g.,
about 3 to 7 percent aluminum; up to about 0.5 percent zirconium;
up to about 1 percent titanium; about 0.1 percent to about 10
percent or more preferably, about 0.25 to 5 percent dispersoid in
the form of a finely divided, well-distributed refractory
dispersoid; such as a refractory oxide, including alumina,
lanthana, yttria, ceria, titania, silica, zirconia, hafnia, for
example; a metal carbide; and/or a metal nitride, such as zirconium
nitride; and the balance essentially iron. Elements such as carbon
and manganese are regarded as impurities and may be present in
amounts up to about 0.4 percent each. The dispersoid particles
preferably have a particle size of about 50A. to 5000A., more
preferably about 100A. to 1000A., and have average interparticle
spacings of about 500A. to about 2500A., more preferably, about
660A. to about 1800A.
More specifically, in one embodiment of the present invention, the
mechanical alloying operation is carried out in a stirred ball
mill, e.g., a Szegvari attritor, provided with an attrition medium
comprising balls having an average diameter of 0.1 to 0.5 inches
and running at an impeller speed of about 50 to 350 RPM. The balls
are present in an amount sufficient to provide a ball-to-powder
ratio, preferably, of about from 4 to 1 to about 50 to 1. It is
preferred that higher impeller speeds be employed in mechanical
alloying with stirred ball mills having relatively small powder
chambers and lower impeller speeds be employed with relatively
large such chambers; for example, with chambers having respective
diameters of about 9 and about 36 inches, the respective impeller
speeds can be about 300 to 400 RPM and about 70 to 100 RPM. The
mechanical alloying operation preferably is carried out for a time
sufficient, in the particular milling device employed, to ensure
the substantial homogeneity of the final composite particles and to
impart substantial saturation hardness to the composite particles.
Experience indicates that milling times of about 10 to about 40
hours, e.g., about 15 to about 20 hours, are usually sufficient in
a high energy mill such as the attritor.
It is preferred that the mechanical alloying operation be conducted
in an inert atmosphere such as argon and, preferably at a flow rate
sufficient to prevent substantial infiltration of air into the
mill, e.g., about 5 cu. ft. of argon per hr. in a mill having an
internal volume of 10 to 15 gallons, so that the uncontrolled
pickup of gases such as oxygen and nitrogen in the powders is
minimized. It appears that the presence of excessive oxygen, and
possibly also nitrogen, in the mill atmosphere during milling can
hinder the welding factor which desirably occurs during mechanical
alloying, may lead to the production of undesirably fine powders
and contribute to inhomogeneity. Preferably, the amount of nitrogen
and of oxygen in the powder, other than that present in the
dispersoid material, due to atmosphere pickup in milling, does not
exceed about 0.4 percent oxygen and 0.2 percent nitrogen.
Satisfactory composite powders generally have average particle
sizes in the range 10 to 1000 microns, e.g., about 20 to 200
microns.
In satisfactory mechanically alloyed, i.e., composite, powders
produced from powder mixtures containing dispersoid powder, the
dispersoid ingredient is present in the powder in a total amount
of, by volume, about 0.1 to 10 percent and is well distributed
throughout the composite at average interparticle distances from
about 500 to 2,500 Angstroms. Once this dispersoid content and
distribution has been established in the powder, it is carried
forward into the consolidated material. It is found that the
characteristic high hardness, or saturation hardness, is developed
in the composite powder after relatively short milling periods and
this hardness will generally be on the order of 630 Vickers
Hardness Number. The composite powder is dense and substantially
devoid of internal porosity such that it withstands penetration by
a diamond pyramid indenter. Generally, milling is continued
substantially beyond the point at which substantial saturation
hardness is achieved in the composite powder for the purpose of
further improving the homogeneity of the powder with beneficial
results in terms of strength and ductility in consolidated powders
made therefrom, as well as avoidance of segregated areas in the
consolidated material made therefrom.
The powder charges that can be converted to mechanically alloyed
powders having the compositional requirements set forth herein, may
include iron powder, e.g., sponge iron, reduced mill scale,
decarburized carbonyl iron powder, etc., generally having a
particle size not exceeding 100 mesh. Chromium may be introduced
into the charge as chromium powder, e.g., electrolytic chromium
having a particle size not exceeding 100 mesh, or ferrochromium
powder containing about 50 to 80 percent chromium and not more than
about 0.2 percent carbon, and the balance iron, having a particle
size not exceeding 100 mesh. Aluminum may be introduced as an
iron-aluminum master alloy powder containing 50 to 80 percent
aluminum and the balance iron and other desired ingredients, e.g.,
iron, chromium, aluminum, etc. Additionally, the chromium and the
aluminum, when desired, can be incorporated into the initial powder
mixture as an iron-chromium-aluminum master alloy powder. It is
preferred that the nitrogen content of the initial powder charge be
sufficiently low to provide mechanically alloyed powder containing
less than 0.2 weight per cent nitrogen.
The mechanically alloyed composite powders are thereafter hot
consolidated as, for example, by canning (in a can which may be
mild steel, stainless steel, nickel, etc., and which is welded shut
after filling with powder) and hot extruding the powder, or by
other hot compaction steps. Powder extrusion can be carried out at
an elevated temperature up to 1600.degree.F. or higher, e.g.,
2000.degree.F. or 2400.degree.F., the extrusion ratio preferably
being about 5:1 to 50:1 or higher. The consolidated powder products
can then be fabricated into various shapes; for example, the
consolidated powder products can be hot and/or cold rolled to plate
or sheet, or rolled, swaged or drawn to bar, rod or wire. Such
fabrication can be carried out at elevated temperatures, e.g., up
to about 2000.degree.F. or even higher, or at ambient temperature,
intermediate anneals preferably being utilized in the latter case
(i.e., fabrication at ambient temperature) after reductions of
about 50 percent.
The consolidated product is then worked (i.e., drawn, forged,
rolled, etc.) at temperatures not exceeding about 1600.degree.F. to
1700.degree.F. so as to permit the production of coarse, elongated
grains on subsequent heat treatment. Heat treatment of the
consolidated product without post-consolidation working thereof
generally does not result in coarse, elongated grains. The required
amount of working of the consolidated product generally decreases
with increasing dispersoid content thereof and is preferably about
10 to 12 percent reduction or more; for example, a cold-working
reduction of about 16 percent to about 25 percent or more can be
employed with a consolidated product having a total dispersoid
content of up to about 1 to 2 volume percent.
In general, the amount of working of the consolidated product
before the grain-coarsening, or secondary recrystallization, heat
treatment and the grain-coarsening heat-treatment temperature that
are required to achieve elongated, relatively coarse grains are a
function of the amount of stored energy in the consolidated
product. Usually, higher amounts of such stored energy can be
produced by mechanically alloying for longer periods of time and/or
consolidating, e.g., by extrusion, the mechanically-alloyed powder
at lower temperatures and/or with greater amounts of working or
deformation of the powder. It is generally desired that the amount
of working before the grain-coarsening heat treatment be sufficient
to induce strains, i.e., provide stored energy, throughout the
consolidated product so that coarse, elongated grains can
subsequently be generated substantially completely throughout the
product.
Following such working, the product is subjected to a
grain-coarsening heat treatment at an elevated temperature which
may be about 2,200.degree.F. up to a temperature below the
incipient melting point of the alloy. In some cases, for example,
when the mechanical alloying operation is conducted for longer
times or when extrusion conditions including extrusion strain rate,
are more severe or when greater amounts of working are
accomplished, or when lower dispersoid contents, e.g, less than
about 1 percent by volume, are present in the consolidated alloy,
the grain-coarsening heat treatment can be conducted at
significantly lower temperatures, e.g., temperatures as low as
1600.degree.F. In terms of stress-rupture properties, it appears
that no significant difference results whether grain coarsening
occurs at a relatively low temperature or at a higher temperature.
Grain coarsening is itself the significant parameter and the
phenomenon does not occur unless work is imparted to the material
after hot consolidation. It is generally found that higher
temperatures are required where the product includes about 0.5
percent or more, by weight, zirconium, or where the powder is
mechanically alloyed for relatively short periods, e.g., about 15
hours. Such heating results in grain growth, wherein the grains of
the product grow to a definite desired size that is not
substantially exceeded even after subsequent sustained exposure to
temperatures approaching the melting point of the alloy, e.g.,
about 2,350.degree.F. to 2,400.degree.F. for 100 hours or more,
which grains are elongated in the direction or directions of
working and generally have dimensions in the range of about 10 to
100 microns wide and about 50 to 2000 microns long, when viewed
two-dimensionally. Such larger grains provide significant
improvement in high temperature tensile and stress-rupture
strengths. Products made according to the invention also exhibit
elevated temperature grain stability, room temperature workability,
comparatively high room-temperature tensile strength, and reduced
tendency for embrittlement at ambient temperatures after extended
exposure to elevated temperature.
As an alternative to the addition of dispersoid particles directly
to the initial powder charge, such dispersoid particles can be
produced by adding precursor material to the initial powder charge
and thereafter converting such precursor material to the
appropriate dispersoid composition. For example, there can be added
to the initial powder charge particles of zirconium metal and/or
misch metal, after which the zirconium and/or misch metal is
converted to the oxide form (i.e., zirconia, lanthana, ceria,
etc.). Such conversion to the dispersoid composition can be
achieved, for example, by introducing controlled amounts of oxygen
into the charge before or during the mechanical alloying operation.
Thus, a readily reducible metal oxide such as iron oxide, nickel
oxide, etc., having a negative free energy of formation
substantially below 90 kilocalories per gram atom of oxygen at
25.degree.C. can be added to the powder charge, or oxygen gas can
be included in a mixture with argon during milling, so as to form a
fine dispersoid oxide by diffusion and internal oxidation when the
resulting powder is hot consolidated. Where the desired dispersoid
particles are nitrides, (e.g. ZrN), controlled amounts of nitrogen
can be introduced into the mill in the form of nitrogen gas mixed
with argon, for example. While oxide and nitride compounds have
been mentioned as dispersoid particle compositions, other types of
dispersoid materials can also be used in the present invention,
e.g., up to about 10 percent of one or more hard phases, such as
carbides, borides, and the like. Refractory compounds which may be
included in the powder mix or produced in situ include oxides,
carbides, nitrides, borides of such refractory metals as thorium,
zirconium, hafnium, titanium, and even such refractory oxides as
those of silicon, aluminum, yttrium, cerium, uranium, magnesium,
calcium, beryllium and the like. In general, the refractory
dispersoid material has a preferred melting point of at least about
2750.degree.F. The refractory oxides generally include the oxides
of those metals whose negative free energy of formation of the
oxide per gram mole of oxygen at about 1000.degree.C. is at least
about 150 kilocalories. The refractory nitrides include those metal
nitrides having a negative free energy of formation of at least
about 25 kilocalories per gram mole of nitrogen at 1000.degree.C.
and the refractory carbides include metal carbides having a
negative free energy of formation of at least about 15 kilocalories
per gram atom of carbon at 1000.degree.C.
EXAMPLE I
8.5 kilograms of a powder mixture comprising, by weight, 28.7
percent minus 100 mesh ferrochromium powder, 1 percent cobalt
powder, having an average particle size of 5 microns, 61 percent
minus 100 mesh iron powder, 6 percent minus 100 mesh ferroaluminum
including 65 percent aluminum, 2.5 percent 100 mesh ferroaluminum
including 65 percent aluminum and 10 percent cerium-free misch
metal, 0.3 percent of ferrocolumbium including 67 percent columbium
and 0.5 percent of ferrozirconium including 10 percent zirconium,
was mechanically alloyed for a period of 18 hours in a 10-gallon
capacity Szegvari attritor. The mechanical alloying was carried out
with 380 lbs. of 5/16-inch diameter steel balls, providing a
ball-to-powder ratio of 20 to 1, at an impeller speed of 180 RPM
and in an argon atmosphere provided by an argon stream flowing at 5
cubic feet per hour. A portion of the mechanically alloyed powder
was canned and extruded at 1950.degree.F. from 31/2 inches to a
3/4-inch diameter bar which had the composition, by weight, 5.7
percent aluminum, 21.5 percent chromium, 0.9 percent cobalt, 0.16
percent manganese, 0.15 percent nickel, 0.016 percent zirconium,
0.035 percent carbon, 0.24 percent oxygen, (% niobium not
determined), 0.12 percent nitrogen, and the balance essentially
iron, the total dispersoid content, including rare earth oxides, of
the bar being about 1 percent. A portion of the extruded bar was
subsequently bar rolled at room temperature to a strain of 40
percent reduction in area, and annealed for one hour at
2400.degree.F. The bar exhibited grain growth as evidenced by
grains having average dimensions of about 100 microns in width and
about 1000 microns in length.
Another portion of the same extruded bar was coldbar rolled by 50
percent reduction in thickness and subjected to a grain-coarsening
heat treatment at 2,400.degree.F. for 2 hours, the resulting grains
(FIG. 1) having an average size of about 2000 microns long by about
100 microns wide. The thus-treated bar survived a step-loaded
stress-rupture test at 1900.degree.F. comprising 162.7 hours at
5,000 psi, 47.9 hours at 6000 psi, 24 hours at 7000 psi, and 24
hours at 8000 psi, with the final duration being 33.4 hours at 9000
psi. The bar broke with 2.5 percent elongation and 7 percent
reduction in area.
EXAMPLE II
An extrusion having the same composition as that described in
Example I was produced with a powder mixture and under the
processing conditions similar to those described in Example I,
except that the mechanical alloying time in this instance was 12
hours. The extrusion, which was fine grained, was turned to a
0.4-inch diameter and drawn at room temperature to a 0.277-inch
diameter rod which was then annealed at 2000.degree.F. for one hour
and further drawn to about 0.1-inch diameter, i.e., a severe
reduction of about 90 percent, without intermediate anneals. The
wire was annealed at 2400.degree.F. for various times of 1/2 to 160
hours, the wire grains, after each of the annealing times being
elongated in the working directions and being, on the average,
about 200 microns long and about 20 microns wide, as illustrated in
FIG. 2, which is the grain structure of the 160 hour annealed wire.
The relative uniformity of grain size of the wires annealed at the
various temperatures indicates the grain stability that is present
therein at elevated temperatures. For comparison, a commercially
available 1/4-inch diameter wire of the composition by weight, 5.55
percent aluminum, 21.0 percent chromium, 0.85 percent cobalt, 0.1
percent manganese, 0.1 percent silicon, 0.25 percent titanium, 0.19
percent nickel, 0.19 percent rare earth metal, balance iron, was
heated at 2400.degree.F. for 170 hours. The commercial wire, which
had an average initial grain size of about 40 microns, exhibited
very extensive, uncontrolled grain growth as a result of the high
temperature heating, the grown grains of the commercial wire being
essentially equiaxed and having an average size of 1200
microns.
To determine the effects of exposure to high temperature or their
room temperature properties, another piece of the above commercial
wire and a second dispersion-strengthened wire, which was similar
in composition to that above and was produced in the manner
described above except that it was grain coarsened by heating for
1/2 hour at 2400.degree.F., were annealed at 2400.degree.F. for
various times and then tested at room temperature. The various
exposure times and the test results are indicated at Table I, from
which it can be seen that the commercial wire is embrittled after
only a short exposure, (i.e., less than 2.5 hours) at
2400.degree.F., but that the grain coarsened wire is strong and
ductile at room temperature even after 120 hours at 2400.degree.F.
The poor ductility of the dispersion-strengthened wire in the
as-drawn condition can be attributed to the severe cold working
that it underwent in the drawing operation.
TABLE I ______________________________________ Room Temperature
Properties ______________________________________ Annealing Time at
2400.degree.F. 0.2% Y.S., U.T.S., El., R.A., (Hours) (ksi) (ksi)
(%) (%) ______________________________________ Commercial 1/4"
Diameter Wire Bar 0 85.3 109 27.5 69.0 2.5 70 78 3.5 2.0 6.0 66 75
2.8 2.2 70.0 67 75 2.0 2.5 170.0 -- 57 <1.0 <1.0 0.10"
Diameter Dispersion-Strengthened Drawn Wire As Drawn 176 204 0.0
0.0 120 86 110 15.0 -- ______________________________________
Another commercial 1/4 inch-diameter wire bar and a third
grain-coarsened 0.10 inch-diameter dispersion strengthened wire,
which had been produced in the above manner and grain coarsened by
heating at 2400.degree.F. for 1/2 hour, were tested at
1900.degree.F. for, respectively, static mechanical properties,
i.e., yield strength (Y.S.), ultimate tensile strength (U.T.S.),
elongation (El.) and reduction in area (R.A.) and stress-rupture
strength, the results being set out in Table II.
TABLE II ______________________________________ 1900.degree.F.
PROPERTIES Commercial Wire 0.2% Y.S., U.T.S., El., R.A., (ksi)
(ksi) (%) (%) ______________________________________ 1.4 2.4 120 95
Dispersion Strengthened Wire Stress Life (ksi) (hrs.) 5 13.3
______________________________________
From these results, it is expected that the commercial wire would
have a 1900.degree.F. stress-rupture life of about zero hours at
stresses of about 2.4 ksi or higher. It appears therefore, that the
grain-coarsened, dispersion-strengthened wire, exhibiting a
1900.degree.F. stress-rupture life at 5 ksi of 13.3 hours, is
considerably superior to the commercial wire under these
conditions.
EXAMPLE III
A portion of the mechanically alloyed powder described in Example I
was canned and hot compacted in a closed extrusion container at
2100.degree.F. to form a 31/2 inch diameter compact having fine
grain size. The compact was heated to 2100.degree.F. and rolled
from 31/2 inch diameter round to a 3-inch square and then to a 2
inch thick rectangle which was cross-rolled to 1-inch thick plate.
The plate was reheated to 2100.degree.F. and rolled to 0.25-inch
plate. The plate was annealed at 1800.degree.F. for 2 hours,
decanned by pickling and then cold-rolled to 0.190 inches, after
which the plate was annealed at 2200.degree.F. for 2 hours and then
cold-rolled to 0.055 inch thick sheet and annealed at
2400.degree.F. for 1/2 hour to achieve grain coarsening. No
difficulty was encountered in either hot or cold rolling. The sheet
exhibits the same type of grain structure as that described in
Example II, i.e., elongated grains of relatively large size (about
200 microns long and 20 microns wide) produced by grain growth.
EXAMPLE IV
Various powder lots having compositions adjusted to provide product
compositions shown in Table III were mechanically alloyed in a
10-gallon capacity Szegvari attritor at an impeller speed of 180
RPM and under a dynamic argon atmosphere flowing at 5 cubic feet
per hour for the mechanical alloying times given in Table III.
TABLE III
__________________________________________________________________________
Element Weight Percent Total Rare Earth Oxide
__________________________________________________________________________
Powder Y.sub.2 O.sub.3 No.(1) C Ni Cr Al Co O N Zr
__________________________________________________________________________
1 .04 .35 21.3 4.6 .93 .37 .09 .10 .18 2 .034 .26 21.7 4.6 .88 .36
.11 .11 .45 3 .025 .26 22.1 4.5 .89 .46 .05 .12 .72 4 .026 .24 20.7
4.3 .85 .35 .06 .03 .45 5 .029 .19 21.5 4.1 .80 .36 .06 .5 .44 6
.026 .21 21.9 4.2 .86 .47 .07 .08 .76 7 .034 .22 21.0 4.2 .79 .48
.09 .06 .76
__________________________________________________________________________
(1) = Powder Nos. 1 through 5, 6, and 7 mechanically alloyed for
15, 24, and 36 hours, respectively. Balance of each powder
essentially iron.
Each mechanically alloyed powder was canned in a 31/2 inch diameter
mild steel can and consolidated without evacuation of the can by
extruding at 2000.degree.F. to 3/4-inch diameter bars, which were
then turned to 0.664-inch diameter. When portions of the bars were
heated at 2400.degree.F. for 1/2 hour in an attempt to achieve
grain coarsening therein, no grain coarsening resulted. Bars
produced from Powder Nos. 1,2,3, 6 and 7 were then individually
rolled at room temperature to various reductions of 16 to 41
percent. A portion of each bar was removed after each reduction
step, each of these portions then being heated at 2400.degree.F.
for 1/2 hour and inspected for grain coarsening, the results being
given in Table IV, where the consolidated products are assigned the
same numbers as their corresponding powders.
The dispersoid particles generally ranged in size from about 150A.
to about 500A., with average interparticle spacings of about 1100A.
for Bar No. 1, about 800A. for Bar Nos. 2,4 and 5, and about 650A.
for Bar Nos. 3,6 and 7, these values occurring in both the
extrusions and in the grain-coarsened products.
TABLE IV ______________________________________ Grain Coarsening
(Percent) COLD REDUCTION Bar No. (2) 0% 16% 25% 35% 41%
______________________________________ 1 0 100 100 100 100 2 0 0
100 100 100 3 0 50 100 100 100 6 0 100 100 100 100 7 0 100 100 100
100 ______________________________________ (2) = Each bar annealed
at 2400.degree.F. for 1/2 hour after cold rolling
From Table IV, the bars that were tested, (i.e., Nos. 1 to 3,6 and
7) did not grain coarsen, i.e., secondary recrystallize, under the
heating conditions employed until some cold deformation was
produced therein. While Bar No. 2 did not grain coarsen until the
cold deformation thereof had reached 25 percent, Bar Nos. 1,6 and 7
were fully grain coarsened and Bar No. 3 was 50 percent grain
coarsened after the 16 percent reduction and heat treatment. Each
one of these bars was fully grain coarsened, i.e., comprised
substantially completely of coarse, elongated grains, after cold
reductions of 25 percent or more and heat treatments at
2,400.degree.F. for 1/2 hour.
EXAMPLE V
Various portions of each one of the extrusions, Nos. 1 through 7,
described in Example IV were cold-rolled to achieve a 25 percent
reduction therein and then heated for 1/2 hour at various
temperatures from 1600.degree.F. to 2400.degree.F., after which the
thus-treated bars were metallographically examined for the presence
of coarse, elongated grains, the results being given in Table
V.
TABLE V ______________________________________ Annealing
Temperature (.degree.F. For 1/2 Hour) Bar No.(3) 1600 1800 1900
2000 2200 2400 ______________________________________ 1 100 100 --
100 -- 100 2 0 0 -- 0 75 100 3 0 0 -- 0 100 100 4 30 100 -- 100 --
100 5 0 0 -- 0 100 100 6 40 50 -- 100 -- 100 7 0 0 20 100 -- 100
______________________________________ (3) = Each bar cold rolled
25% reduction before anneal.
From Table V, all of the bars displayed a relatively coarse,
elongated grain after cold rolling 25 percent reduction and heating
for 1/2 hour at a temperature of 2400.degree.F. Comparing Bars No.
2 and 3 with Bar No. 1, it appears that the grain coarsening
temperature under these conditions, increases with higher
dispersoid contents (Table III). Comparing Bars No. 4 and 5, it
appears that the grain coarsening temperature under these
conditions also increases with higher zirconium contents (see Table
III), the zirconium being thought to form additional dispersoid
material, such as an oxide, carbide or nitride. Comparison of Bars
No. 3 and 6 leads to the conclusion that, under these conditions of
cold work and heat treatment, the temperature needed for total
grain coarsening decreases with longer mechanical alloying
times.
EXAMPLE VI
Various products made from the mechanically alloyed powders
described in Example IV were tested for 1900.degree.F.
stress-rupture in the as-extruded, 25 percent cold worked, and 25
percent cold worked and grain coarsened (annealed at 2400.degree.F.
for 1/2 hour) conditions, the results being given in Table VI,
where the bar numbers are the same as those of the corresponding
powders. Estimated 100-hour rupture stresses are also set out in
Table VI.
TABLE VI
__________________________________________________________________________
1900.degree.F. Stress Rupture (4)
__________________________________________________________________________
Estimated Estimated Estimated Stress for Stress for Cold Worked 25%
Stress for As Extruded 100 Hour Cold Worked 25% 100 Hour Annealed
(1/2-2400.degree.F. ) 100 Hour Bar No. Stress Life Elong. Life
(ksi) Stress Life Elong. Life (ksi) Stress Life Elong. Life
__________________________________________________________________________
(ksi) 1 5 0.4 6.4 2.4 5 3.1 2.4 3.5 7 0.1 8.8 3.5 2 5 6.2 4.0 3.7 5
68.4 4.0 4.8 7 27.5 0.0 6.2 3 5 0.1 33.6 2.5 5 13.3 0.8 4.1 7 17.7
1.2 5.8 4 5 0.1 39.2 2.5 5 >350.0 -- >5.6 7 101.9 2.4 7.0 5 4
1.2 8.8 2.6 5 54.1 1.6 4.7 7 5.1 4.1 5.2 6 4 1.1 9.6 2.6 5 2.0 4.0
3.4 6 1.0 1.6 3.8 7 4 0.5 16.0 2.4 5 2.3 2.4 3.4 7 8.6 3.2 5.4
__________________________________________________________________________
(4) = All stresses in k.s.i.; all lives in hours; all elongations
in %.
From Table VI, it can be seen that cold working to a 25 percent
reduction generally results in increased 1900.degree.F.
stress-rupture strengths and that the grain coarsened bars
demonstrate further increases in 1900.degree.F. stress-rupture
strength. It is noted from Table V that specimens (Bars No. 1 and
4) corresponding to Bars No. 1 and 4 of Table VI grain coarsen at
temperatures below 1900.degree.F., so that these Bars No. 1 and 4
in the cold-worked condition grain coarsened on heating up to the
1900.degree.F. test temperature and the subsequent 2400.degree.F.
anneal for 1/2 hour had no apparent beneficial effect on their
strength properties.
Although the present invention has been described in conjunction
with preferred embodiments, it is to be understood that
modifications and variations may be resorted to without departing
from the spirit and scope of the invention, as those skilled in the
art will readily understand. Such modifications and variations are
considered to be within the purview and scope of the invention and
appended claims.
* * * * *