CA1232780A - Work-hardenable austenitic manganese steel and method for the production thereof - Google Patents
Work-hardenable austenitic manganese steel and method for the production thereofInfo
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- C22—METALLURGY; FERROUS OR NON-FERROUS ALLOYS; TREATMENT OF ALLOYS OR NON-FERROUS METALS
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- C22C38/00—Ferrous alloys, e.g. steel alloys
- C22C38/04—Ferrous alloys, e.g. steel alloys containing manganese
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Abstract
ABSTRACT OF THE DISCLOSURE
A work-hardenable austenitic manganese steel has a base composition (each in percent by weight) of 0.8 to 1.8 carbon, 6.0 to 18.0 manganese, 0 to 3.0 chromium, 0 to 2.0 nickel, 0 to 2.5 molybdenum and 0 to 1 silicon.
The ratio of carbon to manganese is in the range of 1 : 8 to 1 : 14, the remainder being iron, impurities, deoxidation additions and micro-alloying elements. The micro-alloying elements employed are vanadium and titanium, the total amount of the vanadium and titanium content being limited to the range of 0.05 to 0.08 percent by weight. The contents of vanadium and titanium should preferably be at least 0.01 percent by weight each, and more preferably at least 0.02 percent by weight each. The inclusion of vanadium and titanium brings about a reduction in grain size over the entire cross section of even large castings of work-hardenable austenitic manganese steel without impairing their mechanical properties, particularly their toughness. The steel is cold workable, and is work-hardenable by cold working. The deoxidation additions consist mainly of aluminum, and aluminum content of 0.02 to 0,09 percent by weight should remain in the steel after deoxidation.
A work-hardenable austenitic manganese steel has a base composition (each in percent by weight) of 0.8 to 1.8 carbon, 6.0 to 18.0 manganese, 0 to 3.0 chromium, 0 to 2.0 nickel, 0 to 2.5 molybdenum and 0 to 1 silicon.
The ratio of carbon to manganese is in the range of 1 : 8 to 1 : 14, the remainder being iron, impurities, deoxidation additions and micro-alloying elements. The micro-alloying elements employed are vanadium and titanium, the total amount of the vanadium and titanium content being limited to the range of 0.05 to 0.08 percent by weight. The contents of vanadium and titanium should preferably be at least 0.01 percent by weight each, and more preferably at least 0.02 percent by weight each. The inclusion of vanadium and titanium brings about a reduction in grain size over the entire cross section of even large castings of work-hardenable austenitic manganese steel without impairing their mechanical properties, particularly their toughness. The steel is cold workable, and is work-hardenable by cold working. The deoxidation additions consist mainly of aluminum, and aluminum content of 0.02 to 0,09 percent by weight should remain in the steel after deoxidation.
Description
This invention relates to a work-hardenable austenitic manganese steel of a base composition (each in percent by weight) of 0.8 to 1.8 carbon, 6.0 to 18.0 manganese, 0 to 3.0 chromium, 0 to 2.0 nickel, 0 to 2.5 molybdenum and 0 to 1.0 silicon. The ratio of carbon to manganese is in the range of 1 : 8 to 1 : 14 and the remainder consists of iron, impurities, deoxidation additions and micro-alloying elements such as vanadium and titanium.
A work-hardenable austenitic manganese steel of this type is characterized by very high hardness, and, above all, by its suitability for work-hardening by cold working. It can further harden in due course during use due to mechanical stress by shock, impact or pressure. Mechanical stress leads to martensitic conversion in a surface layer, with the hardness in this layer rising to 200, and up to more than 500, in Brinell hardness. The hard surface layer is removed by stress, but is constantly renewed by this very stress. The material under the surface layer is very tough and highly ductile. For this reason these work-hardenable austenitic manganese steels can withstand high impact stress. As a result, they are used for mining and dressing tools, bullet-proof armor plating, steel helmets and the like.
A prerequisite for the favorable mechanical properties, in particular for the ductility of the material under the hard surface layer, is a fine grain. This fine grain is difficult to attain, particularly inside of larger castings. Large castings have very different grain sizes along their cross sections: a fine-grained edge zone is followed by a zone consisting of coarse columnar crystals, followed, in turn, by the globulitic structure at the center of the casting. Even forging of the casting cannot compensate for the differences in grain. Compensation is particularly difficult in the case of dead-mold castings. Elongation and notched bar impact strength is not always adequate, even with strict observation of the alloy composition desiderata.
I Q
It is known to subject ingots or dead-mold castings to heat treat-mint in order to reduce their grain size This heat treatment consists of a first annealing lasting many hours, at temperatures of 500 to 600 C, in order to convert austenite to puerility, and of a second annealing step at 970 to 1110C for the reconversion to austenite. The effect of this operation, in spite of its elaborateness, is insecure.
It is further known to pour the melt off at very low casting temperatures close to the melting temperatures. The low casting temperature brings about a large number of nuclei and a finer grain. This process entails great practical difficulties and allows only simple shapes since the melt does not completely fill up remote spots or edges of the casting mold in the liquid state.
It is further known to achieve grain refining by the addition of carbide- or nitride-forming elements such as Tip Or, Nub, V, B and/or N to the steel, the amounts added being at least 0.1 and 0.2 percent by weight each.
These micro-alloying elements do result in a reduction of the grain size, but at the same time they reduce elongation and notch-impact strength.
According to an unpublished proposal, Tip Or and V may be added as micro-alloying elements, each in an amount of up to 0.05 percent by weight, the sum of contents of these micro-alloying elements to amount to 0.002 to 0.05 percent by weight. This proposal has, however, also turned out to be of little practical value in large-scale industrial application. The expected fine grain in the cold-worked work-hardenable austenitic manganese steel simply did not materialize in actual practice in many cases.
The present invention is based on a work-hardenable austenitic manganese steel such so it is described in DIN standard material No. 1.3401.
According to this standard, the alloy contents in percent by weight are the following: C about 1.25, My 11 to 14, Or up to 2.5, No up to 2 for the stabilization of the austenite, and My up to 2.5 to prevent coarse precipita-lion of carbide. The ratio of carbon content to manganese content must be 1 : 8 to 1 : 14, which means that the manganese - adjusted to the carbon con-tent - must suffice for an austenite structure, on the one hand, and must not stabilize the austenite so strongly that work-hardening by cold working is impaired, on the other hand.
It is the object of the invention to provide a work-hardenable austenitic manganese steel which is work-hardenable by cold working and is uniformly ductile and finegrained over its entire cross-section and at the same time free of disadvantages such as those described above. The elongation at rupture should be at least 20 percent and the remaining mechanical properties should not deteriorate.
This object is achieved in a steel of the type identified above by keeping the sum of the contents of vanadium and titanium at to 0.08 percent by weight. By adhering to this condition, the attempted improvement of the mechanical properties of the work-hardenable austenitic manganese steel is non-dewed safely reproducible even when carried out on a large industrial scale.
Surprisingly, the desired fine grain is achieved over the entire cross-section of the casting without deterioration of the remaining mechanical properties.
It was surprisingly found that it is of advantage to keep the contents of vanadium and titanium of the steel according to the invention at 0.01 percent by weight each, in particular at 0.02 percent by weight each.
An aluminum content of 0.02 to 0.09 percent by weight is preferred as a residual aluminum content after deoxidation so as to assure a complete deoxidation which is necessary prior to the addition of titanium.
In the production of the work-hardenable austenitic manganese steel according to the invention, in which the micro-alloying elements are added after melting of the charge in the electric furnace or in the casting ladle, and the casting is subjected to heat treatment after removal from the mold, the vanadium is preferably added to the charge in the electric furnace at the end of the refining period and the titanium is added to the charge in the casting ladle after deoxidation of the same by means of aluminum. It is also possible, however, to add the titanium as well as the vanadium to the charge in the casting ladle. The heat treatment preferably comprises annealing at temperatures of 1050 to 1150C followed by fast cooling.
Prior to deoxidation and adjustment of the desired tapping tempera-lure to a range of 1450 to 1620C, the melt is covered by lime-containing slag in order to be able to maintain the casting temperature in the casting ladle within a range of 1420 to 1520C. The previously mentioned heat treat-mint of the ingots or dead-mold castings is useful for the compensation of the mechanical properties uniformly over the entire cross-section of the casting. Cooling of the casting can be effected in a water bath and/or air stream, optionally preceded by a first, slower cooling step.
The invention will now be explained in detail with the aid of the following examples.
Example 1:
3000 kg of manganese steel of the following composition were melted in an arc-furnace:
1.30 percent by weight of carbon, 13.60 percent by weight of manganese, 0.10 percent by weight of chromium, 0.22 percent by weight of silicon. At the end of the refining period, 1.5 kg (0.04 percent by weight) of vanadium were added in the form of ferrovanadium. The melt was then covered by a lime-containing slag, a tapping temperature of 1510C was measured and 2 kg of aluminum were added for deoxidation. At tapping, six casting ladles were filled with a content of about 200 kg melt each. The following amounts of titanium were added to the six casting ladles ( in the form of ferrotitani.u"l) and the casting temperature in each ladle was measured with the following results:
Casting ladle A: titanium addition 0 kg casting temperature 1440C
Ladle B: titanium addition 0.04 kg casting temperature 1445C
Ladle C: titanium addition 0.06 kg casting temperature 1445 C
Ladle D: titanium addition 0.08 kg casting temperature 1440 C
Ladle E: titanium addition 0.11 kg casting temperature 1395 C
Ladle F: titanium addition 0.13 kg casting temperature 1400 C
Of the metal of each one of the six casting ladles, three each round rods with a diameter of 15 cm and a length of 1 meter were cast. The 18 rods were taken from the mold and cooled and then kept in an annealing furnace for four hours at a temperature of 1070C. The rods were cooled in a water bath immediately after removal from the furnace. Of each one of the rods, one each sample was taken at distances of 20, 50 and 70 cm from the (at casting) lower end, from the edge and from the center of the rods, and photo micro graphs from the sample zone of the rods were made. All 54 samples (of which three each are of the same composition and taken from the identical spot) were subjected to testing as to strength and cold workability by I
determining their tensile strength and elongation at rupture. moreover the vanadium content of all the samples (which was nearly identical in all of them) was determined to be 0.038 to 0.041 percent by weight, two each samples from one and the same casting ladle were analyzed as to their titanium content.
The titanium contents in the following table are the average values formed of the two each analyses. The table also shows the average values of the mechanical data determined in the three easily parallel samples.
-Titanium content Place of taking percent by weight sample at height tensile strength elongation at (designation of of my rupture (%) casting ladle) 20 cm (bottom) 50 cm (center) 70 cm (top) center edge center edge 0 bottom 720 750 27 41 (A) center 760 760 25 37 top 760 790 20 23 0.014 bottom 720 720 40 49 (B) center 710 730 29 42 top 740 680 35 41 0.022 bottom 660 680 49 53 (C) center 630 680 42 44 top 630 670 43 42 0.036 bottom 730 740 61 62 (D) center 820 780 51 59 top I 70 42 53 0.045 bottom 720 760 33 48 (~) center 700 720 27 42 top 690 710 17 29 0.053 bottom 700 720 20 31 (F) center 690 710 18 28 top 770 710 21 30 It is evident that in the absence of titanium (casting ladle A) and at the titanium contents of casting ladles E and F (0.045 and 0.053 percent by weight, respectively) which show a sum of the vanadium and titanium content below and above the range according to the present invention, the elongation at rupture is not always above the attempted minimum value of 20 percent. The samples with the unfavorable values of elongation at rupture (casting ladles A and E top and casting ladle F center and top) range above the sought minimum value at the average indicated in the table, at least partly, but the elongations at rupture actually achieved in these samples are below 20% in the unfavorable cases and generally lower than in the samples of casting ladles I, C, D. Photo-micrographs also reflected this result. In the samples with the lowest values of elongation at rupture, average grain size distributions of 0.5 mm up to more than 8.0 mm were determined. In the samples with the values of elongation at rupture in the desired range, of more than 20 percent, the average grain size distribution did not exceed 0.5 mm in any case.
Example _ 3200 kg of manganese steel of the following composition were melted in an arc-furnace:
1.14 percent by weight of carbon, 13.50 percent by weight of manganese, 0.46 percent by weight of chromium, 0.48 percent by weight of silicon.
At the end of the refining period, 1.6 kg of vanadium (0.05 percent by weight in the form of ferrovanadium) were added. After covering the melt with slag of limestone with an addition of calcium fluoride, a tapping temperature of 1580C was measured and aluminum was added for deoxidation.
After the subsequent tapping into the casting ladle, the titanium content in the ladle was adjusted to 0.015 percent by weight by adding ferrotitanium.
At a casting temperature of 1490C, crusher jaws with a maximum wall thickness of 180 mm intended for installation in an ore crusher were cast. The cooled castings were removed from the mold and annealed at a temperature of 1120 C
for three hours. After annealing, the castings were immediately quenched in water.
Samples from the core and the edge zone were taken from five of the I
finished castings prepared in an identical manner. Photo-micrographs were made and the tensile strength and elongation at rupture of the sample material was determined. The tensile strength of all the samples was in a range of 760 to 790 N/mm . The values of elongation at rupture ranged between 47 and 55 percent; the dispersion of results being independent of the site of taking the sample, i.e. the samples taken from the core of the castings were on the average not less cold workable than the samples taken from the edge zones.
This finding was confirmed by the yhoto-micrographs. There was hardly any difference in the grain size between the samples taken from the core and the lo edge zone; the samples were fined-grained without exception.
The analysis revealed the following contents of vanadium, titanium and aluminum: 0.045 percent by weight of vanadium, 0.015 percent by weight of titanium, 0.03 percent by weight of aluminum.
A work-hardenable austenitic manganese steel of this type is characterized by very high hardness, and, above all, by its suitability for work-hardening by cold working. It can further harden in due course during use due to mechanical stress by shock, impact or pressure. Mechanical stress leads to martensitic conversion in a surface layer, with the hardness in this layer rising to 200, and up to more than 500, in Brinell hardness. The hard surface layer is removed by stress, but is constantly renewed by this very stress. The material under the surface layer is very tough and highly ductile. For this reason these work-hardenable austenitic manganese steels can withstand high impact stress. As a result, they are used for mining and dressing tools, bullet-proof armor plating, steel helmets and the like.
A prerequisite for the favorable mechanical properties, in particular for the ductility of the material under the hard surface layer, is a fine grain. This fine grain is difficult to attain, particularly inside of larger castings. Large castings have very different grain sizes along their cross sections: a fine-grained edge zone is followed by a zone consisting of coarse columnar crystals, followed, in turn, by the globulitic structure at the center of the casting. Even forging of the casting cannot compensate for the differences in grain. Compensation is particularly difficult in the case of dead-mold castings. Elongation and notched bar impact strength is not always adequate, even with strict observation of the alloy composition desiderata.
I Q
It is known to subject ingots or dead-mold castings to heat treat-mint in order to reduce their grain size This heat treatment consists of a first annealing lasting many hours, at temperatures of 500 to 600 C, in order to convert austenite to puerility, and of a second annealing step at 970 to 1110C for the reconversion to austenite. The effect of this operation, in spite of its elaborateness, is insecure.
It is further known to pour the melt off at very low casting temperatures close to the melting temperatures. The low casting temperature brings about a large number of nuclei and a finer grain. This process entails great practical difficulties and allows only simple shapes since the melt does not completely fill up remote spots or edges of the casting mold in the liquid state.
It is further known to achieve grain refining by the addition of carbide- or nitride-forming elements such as Tip Or, Nub, V, B and/or N to the steel, the amounts added being at least 0.1 and 0.2 percent by weight each.
These micro-alloying elements do result in a reduction of the grain size, but at the same time they reduce elongation and notch-impact strength.
According to an unpublished proposal, Tip Or and V may be added as micro-alloying elements, each in an amount of up to 0.05 percent by weight, the sum of contents of these micro-alloying elements to amount to 0.002 to 0.05 percent by weight. This proposal has, however, also turned out to be of little practical value in large-scale industrial application. The expected fine grain in the cold-worked work-hardenable austenitic manganese steel simply did not materialize in actual practice in many cases.
The present invention is based on a work-hardenable austenitic manganese steel such so it is described in DIN standard material No. 1.3401.
According to this standard, the alloy contents in percent by weight are the following: C about 1.25, My 11 to 14, Or up to 2.5, No up to 2 for the stabilization of the austenite, and My up to 2.5 to prevent coarse precipita-lion of carbide. The ratio of carbon content to manganese content must be 1 : 8 to 1 : 14, which means that the manganese - adjusted to the carbon con-tent - must suffice for an austenite structure, on the one hand, and must not stabilize the austenite so strongly that work-hardening by cold working is impaired, on the other hand.
It is the object of the invention to provide a work-hardenable austenitic manganese steel which is work-hardenable by cold working and is uniformly ductile and finegrained over its entire cross-section and at the same time free of disadvantages such as those described above. The elongation at rupture should be at least 20 percent and the remaining mechanical properties should not deteriorate.
This object is achieved in a steel of the type identified above by keeping the sum of the contents of vanadium and titanium at to 0.08 percent by weight. By adhering to this condition, the attempted improvement of the mechanical properties of the work-hardenable austenitic manganese steel is non-dewed safely reproducible even when carried out on a large industrial scale.
Surprisingly, the desired fine grain is achieved over the entire cross-section of the casting without deterioration of the remaining mechanical properties.
It was surprisingly found that it is of advantage to keep the contents of vanadium and titanium of the steel according to the invention at 0.01 percent by weight each, in particular at 0.02 percent by weight each.
An aluminum content of 0.02 to 0.09 percent by weight is preferred as a residual aluminum content after deoxidation so as to assure a complete deoxidation which is necessary prior to the addition of titanium.
In the production of the work-hardenable austenitic manganese steel according to the invention, in which the micro-alloying elements are added after melting of the charge in the electric furnace or in the casting ladle, and the casting is subjected to heat treatment after removal from the mold, the vanadium is preferably added to the charge in the electric furnace at the end of the refining period and the titanium is added to the charge in the casting ladle after deoxidation of the same by means of aluminum. It is also possible, however, to add the titanium as well as the vanadium to the charge in the casting ladle. The heat treatment preferably comprises annealing at temperatures of 1050 to 1150C followed by fast cooling.
Prior to deoxidation and adjustment of the desired tapping tempera-lure to a range of 1450 to 1620C, the melt is covered by lime-containing slag in order to be able to maintain the casting temperature in the casting ladle within a range of 1420 to 1520C. The previously mentioned heat treat-mint of the ingots or dead-mold castings is useful for the compensation of the mechanical properties uniformly over the entire cross-section of the casting. Cooling of the casting can be effected in a water bath and/or air stream, optionally preceded by a first, slower cooling step.
The invention will now be explained in detail with the aid of the following examples.
Example 1:
3000 kg of manganese steel of the following composition were melted in an arc-furnace:
1.30 percent by weight of carbon, 13.60 percent by weight of manganese, 0.10 percent by weight of chromium, 0.22 percent by weight of silicon. At the end of the refining period, 1.5 kg (0.04 percent by weight) of vanadium were added in the form of ferrovanadium. The melt was then covered by a lime-containing slag, a tapping temperature of 1510C was measured and 2 kg of aluminum were added for deoxidation. At tapping, six casting ladles were filled with a content of about 200 kg melt each. The following amounts of titanium were added to the six casting ladles ( in the form of ferrotitani.u"l) and the casting temperature in each ladle was measured with the following results:
Casting ladle A: titanium addition 0 kg casting temperature 1440C
Ladle B: titanium addition 0.04 kg casting temperature 1445C
Ladle C: titanium addition 0.06 kg casting temperature 1445 C
Ladle D: titanium addition 0.08 kg casting temperature 1440 C
Ladle E: titanium addition 0.11 kg casting temperature 1395 C
Ladle F: titanium addition 0.13 kg casting temperature 1400 C
Of the metal of each one of the six casting ladles, three each round rods with a diameter of 15 cm and a length of 1 meter were cast. The 18 rods were taken from the mold and cooled and then kept in an annealing furnace for four hours at a temperature of 1070C. The rods were cooled in a water bath immediately after removal from the furnace. Of each one of the rods, one each sample was taken at distances of 20, 50 and 70 cm from the (at casting) lower end, from the edge and from the center of the rods, and photo micro graphs from the sample zone of the rods were made. All 54 samples (of which three each are of the same composition and taken from the identical spot) were subjected to testing as to strength and cold workability by I
determining their tensile strength and elongation at rupture. moreover the vanadium content of all the samples (which was nearly identical in all of them) was determined to be 0.038 to 0.041 percent by weight, two each samples from one and the same casting ladle were analyzed as to their titanium content.
The titanium contents in the following table are the average values formed of the two each analyses. The table also shows the average values of the mechanical data determined in the three easily parallel samples.
-Titanium content Place of taking percent by weight sample at height tensile strength elongation at (designation of of my rupture (%) casting ladle) 20 cm (bottom) 50 cm (center) 70 cm (top) center edge center edge 0 bottom 720 750 27 41 (A) center 760 760 25 37 top 760 790 20 23 0.014 bottom 720 720 40 49 (B) center 710 730 29 42 top 740 680 35 41 0.022 bottom 660 680 49 53 (C) center 630 680 42 44 top 630 670 43 42 0.036 bottom 730 740 61 62 (D) center 820 780 51 59 top I 70 42 53 0.045 bottom 720 760 33 48 (~) center 700 720 27 42 top 690 710 17 29 0.053 bottom 700 720 20 31 (F) center 690 710 18 28 top 770 710 21 30 It is evident that in the absence of titanium (casting ladle A) and at the titanium contents of casting ladles E and F (0.045 and 0.053 percent by weight, respectively) which show a sum of the vanadium and titanium content below and above the range according to the present invention, the elongation at rupture is not always above the attempted minimum value of 20 percent. The samples with the unfavorable values of elongation at rupture (casting ladles A and E top and casting ladle F center and top) range above the sought minimum value at the average indicated in the table, at least partly, but the elongations at rupture actually achieved in these samples are below 20% in the unfavorable cases and generally lower than in the samples of casting ladles I, C, D. Photo-micrographs also reflected this result. In the samples with the lowest values of elongation at rupture, average grain size distributions of 0.5 mm up to more than 8.0 mm were determined. In the samples with the values of elongation at rupture in the desired range, of more than 20 percent, the average grain size distribution did not exceed 0.5 mm in any case.
Example _ 3200 kg of manganese steel of the following composition were melted in an arc-furnace:
1.14 percent by weight of carbon, 13.50 percent by weight of manganese, 0.46 percent by weight of chromium, 0.48 percent by weight of silicon.
At the end of the refining period, 1.6 kg of vanadium (0.05 percent by weight in the form of ferrovanadium) were added. After covering the melt with slag of limestone with an addition of calcium fluoride, a tapping temperature of 1580C was measured and aluminum was added for deoxidation.
After the subsequent tapping into the casting ladle, the titanium content in the ladle was adjusted to 0.015 percent by weight by adding ferrotitanium.
At a casting temperature of 1490C, crusher jaws with a maximum wall thickness of 180 mm intended for installation in an ore crusher were cast. The cooled castings were removed from the mold and annealed at a temperature of 1120 C
for three hours. After annealing, the castings were immediately quenched in water.
Samples from the core and the edge zone were taken from five of the I
finished castings prepared in an identical manner. Photo-micrographs were made and the tensile strength and elongation at rupture of the sample material was determined. The tensile strength of all the samples was in a range of 760 to 790 N/mm . The values of elongation at rupture ranged between 47 and 55 percent; the dispersion of results being independent of the site of taking the sample, i.e. the samples taken from the core of the castings were on the average not less cold workable than the samples taken from the edge zones.
This finding was confirmed by the yhoto-micrographs. There was hardly any difference in the grain size between the samples taken from the core and the lo edge zone; the samples were fined-grained without exception.
The analysis revealed the following contents of vanadium, titanium and aluminum: 0.045 percent by weight of vanadium, 0.015 percent by weight of titanium, 0.03 percent by weight of aluminum.
Claims (5)
PROPERTY OR PRIVILEGE IS CLAIMED ARE DEFINED AS FOLLOWS:
1. A work-hardenable austenitic manganese steel having the following alloy contents in percent by weight:
0.8 to 1.8 C
6.0 to 18.0 Mn 0 to 3.0 Cr 0 to 2.0 Ni 0 to 2.5 Mo 0 to 1.0 Si with the ratio of carbon to manganese in the range of 1 : 8 to 1 : 14, the remainder consisting of iron, impurities, deoxidation additions and micro-alloying elements such as vanadium and titanium, characterized in that the sum of the vanadium and titanium contents amounts to 0.05 to 0.08 percent by weight.
0.8 to 1.8 C
6.0 to 18.0 Mn 0 to 3.0 Cr 0 to 2.0 Ni 0 to 2.5 Mo 0 to 1.0 Si with the ratio of carbon to manganese in the range of 1 : 8 to 1 : 14, the remainder consisting of iron, impurities, deoxidation additions and micro-alloying elements such as vanadium and titanium, characterized in that the sum of the vanadium and titanium contents amounts to 0.05 to 0.08 percent by weight.
2. Work-hardenable austenitic manganese steel according to claim 1, wherein the contents of vanadium and titanium amount to at least 0.01 percent by weight each.
3. Work-hardenable austenitic manganese steel according to claim 1, wherein the contents of vanadium and titanium amount to at least 0.02 percent by weight each.
4. Work-hardenable austenitic manganese steel according to claim 1, or 2, or 3, wherein the aluminum content amounts to 0.02 to 0.09 percent by weight.
5. A method for the production of the work-hardenable austenitic manganese steel of the nature defined in claim 1, or 2, or 3, which method comprising adding the micro-alloying elements after melting of the charge to an electric furnace or to a casting ladle, and then subjecting the resultant casting to heat treatment after removal from the mold, the vanadium being added to the melt present in the electric furnace at the end of the refining period and the titanium being added to the melt present in the casting ladle after deoxidation of the melt by means of aluminum, the said heat treatment includ-ing the steps of annealing at temperatures of 1050 to 1150°C and cooling rapid-ly after annealing.
Applications Claiming Priority (2)
| Application Number | Priority Date | Filing Date | Title |
|---|---|---|---|
| AT0339283A AT390806B (en) | 1983-09-23 | 1983-09-23 | AUSTENITIC MANGANIC STEEL AND METHOD FOR THE PRODUCTION THEREOF |
| AT3392/83 | 1983-09-23 |
Publications (1)
| Publication Number | Publication Date |
|---|---|
| CA1232780A true CA1232780A (en) | 1988-02-16 |
Family
ID=3549847
Family Applications (1)
| Application Number | Title | Priority Date | Filing Date |
|---|---|---|---|
| CA000463742A Expired CA1232780A (en) | 1983-09-23 | 1984-09-21 | Work-hardenable austenitic manganese steel and method for the production thereof |
Country Status (14)
| Country | Link |
|---|---|
| EP (1) | EP0143873B1 (en) |
| JP (1) | JPS6089549A (en) |
| AT (2) | AT390806B (en) |
| AU (1) | AU569322B2 (en) |
| BR (1) | BR8404765A (en) |
| CA (1) | CA1232780A (en) |
| DE (1) | DE3471327D1 (en) |
| ES (1) | ES8606909A1 (en) |
| IN (1) | IN161686B (en) |
| MX (1) | MX161638A (en) |
| NO (1) | NO843829L (en) |
| PH (1) | PH20706A (en) |
| ZA (1) | ZA846566B (en) |
| ZW (1) | ZW15584A1 (en) |
Cited By (2)
| Publication number | Priority date | Publication date | Assignee | Title |
|---|---|---|---|---|
| US5595614A (en) * | 1995-01-24 | 1997-01-21 | Caterpillar Inc. | Deep hardening boron steel article having improved fracture toughness and wear characteristics |
| US6572713B2 (en) | 2000-10-19 | 2003-06-03 | The Frog Switch And Manufacturing Company | Grain-refined austenitic manganese steel casting having microadditions of vanadium and titanium and method of manufacturing |
Families Citing this family (8)
| Publication number | Priority date | Publication date | Assignee | Title |
|---|---|---|---|---|
| CA1221560A (en) * | 1983-10-14 | 1987-05-12 | Bernd Kos | Work-hardenable austenitic manganese steel and method for the production thereof |
| DE3628395C1 (en) * | 1986-08-21 | 1988-03-03 | Thyssen Edelstahlwerke Ag | Use of steel for plastic molds |
| JPS63252676A (en) * | 1987-04-08 | 1988-10-19 | Ube Ind Ltd | Mechanical parts having excellent rolling fatigue characteristic and its production |
| FR2666351B1 (en) * | 1990-08-29 | 1993-11-12 | Creusot Loire Industrie | PROCESS FOR THE DEVELOPMENT OF A TOOL STEEL, ESPECIALLY FOR THE MANUFACTURE OF MOLDS AND STEEL OBTAINED BY THIS PROCESS. |
| FI904500A (en) * | 1990-09-12 | 1992-03-13 | Lokomo Oy | SLITSTARKET STAOL OCH FOERFARANDE FOER FRAMSTAELLNING AV DETTA. |
| US5601782A (en) * | 1992-06-26 | 1997-02-11 | Shinhokoku Steel Corporation | Abrasive resistant high manganese cast steel |
| US5865385A (en) * | 1997-02-21 | 1999-02-02 | Arnett; Charles R. | Comminuting media comprising martensitic/austenitic steel containing retained work-transformable austenite |
| DE10016798B4 (en) * | 2000-04-05 | 2006-05-04 | Volkswagen Ag | Use of a hot-rolled, wear-resistant austenitic manganese steel sheet |
Family Cites Families (8)
| Publication number | Priority date | Publication date | Assignee | Title |
|---|---|---|---|---|
| GB1187023A (en) * | 1966-05-09 | 1970-04-08 | Hadfields Ltd | Improvements in Wear-Resisting Steel. |
| SU322399A1 (en) * | 1970-07-03 | 1971-11-30 | ||
| DE2535519C3 (en) * | 1975-08-08 | 1985-06-20 | Rubcovskij zavod traktornych zapasnych Častej, Rubcovsk | Use of steel as a material for the manufacture of components on machines that are exposed to heavy loads, intensive wear and tear and sub-zero temperatures during operation |
| SU610879A1 (en) * | 1976-05-24 | 1978-06-15 | Уральский научно-исследовательский институт черных металлов | Steel |
| SU581165A1 (en) * | 1976-06-16 | 1977-11-25 | Уральский научно-исследовательский институт черных металлов | Wear-resistant steel |
| FR2402714A1 (en) * | 1977-09-07 | 1979-04-06 | Strommen Staal As | Austenitic steel resistant to wear combined with shock - contains high percentage of manganese, plus carbon, chromium and titanium (DK 2.4.79) |
| AT377287B (en) * | 1982-04-13 | 1985-02-25 | Ver Edelstahlwerke Ag | COLD-STRENGING AUSTENITIC MANGANIC STEEL AND METHOD FOR PRODUCING THE SAME |
| CA1221560A (en) * | 1983-10-14 | 1987-05-12 | Bernd Kos | Work-hardenable austenitic manganese steel and method for the production thereof |
-
1983
- 1983-09-23 AT AT0339283A patent/AT390806B/en not_active IP Right Cessation
-
1984
- 1984-05-02 AT AT84104916T patent/ATE34411T1/en not_active IP Right Cessation
- 1984-05-02 EP EP84104916A patent/EP0143873B1/en not_active Expired
- 1984-05-02 DE DE8484104916T patent/DE3471327D1/en not_active Expired
- 1984-08-23 ZA ZA846566A patent/ZA846566B/en unknown
- 1984-08-28 ES ES535477A patent/ES8606909A1/en not_active Expired
- 1984-09-03 IN IN671/MAS/84A patent/IN161686B/en unknown
- 1984-09-04 PH PH31179A patent/PH20706A/en unknown
- 1984-09-10 AU AU32863/84A patent/AU569322B2/en not_active Ceased
- 1984-09-13 ZW ZW155/84A patent/ZW15584A1/en unknown
- 1984-09-13 JP JP59192443A patent/JPS6089549A/en active Pending
- 1984-09-17 MX MX202716A patent/MX161638A/en unknown
- 1984-09-21 CA CA000463742A patent/CA1232780A/en not_active Expired
- 1984-09-21 BR BR8404765A patent/BR8404765A/en unknown
- 1984-09-24 NO NO843829A patent/NO843829L/en unknown
Cited By (2)
| Publication number | Priority date | Publication date | Assignee | Title |
|---|---|---|---|---|
| US5595614A (en) * | 1995-01-24 | 1997-01-21 | Caterpillar Inc. | Deep hardening boron steel article having improved fracture toughness and wear characteristics |
| US6572713B2 (en) | 2000-10-19 | 2003-06-03 | The Frog Switch And Manufacturing Company | Grain-refined austenitic manganese steel casting having microadditions of vanadium and titanium and method of manufacturing |
Also Published As
| Publication number | Publication date |
|---|---|
| DE3471327D1 (en) | 1988-06-23 |
| ATA339283A (en) | 1989-12-15 |
| ZW15584A1 (en) | 1984-12-05 |
| JPS6089549A (en) | 1985-05-20 |
| PH20706A (en) | 1987-03-30 |
| AT390806B (en) | 1990-07-10 |
| EP0143873B1 (en) | 1988-05-18 |
| MX161638A (en) | 1990-11-27 |
| ES535477A0 (en) | 1986-05-16 |
| ZA846566B (en) | 1985-04-24 |
| IN161686B (en) | 1988-01-16 |
| NO843829L (en) | 1985-03-25 |
| EP0143873A1 (en) | 1985-06-12 |
| ES8606909A1 (en) | 1986-05-16 |
| BR8404765A (en) | 1985-08-13 |
| AU3286384A (en) | 1985-03-28 |
| AU569322B2 (en) | 1988-01-28 |
| ATE34411T1 (en) | 1988-06-15 |
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