TOOL STEEL

Abstract: A tool steel, comprising high speed steel and cold working steel, produced from metal powder by compaction at a high pressure and a high temperature to full density. The steel is characterized in that a) at least 40% of the carbides of a randomly chosen section have a largest extension > 1.5 mu m, b) at least 25% of the carbide area of a randomly chosen section is contributed by carbides with an extension > 3 mu m, c) the steel contains carbides, the maximum size Lmax of these carbides and/or of carbide aggregates being a function of the diameter or smallest gauge of the product, and that d) the steel contains at least 0.7% carbon and at least 10% of one or several of the following metals: chromium, tungsten, molybdenum, and vanadium, or mixtures of these.

Description: TOOL STEEL TECHNICAL SCOPE The invention relates to tool steel made from metal powder by compacting said powder at a high pressure and a high temperature to full density. Particularly, the invention relates to high speed steel, but the principles of the invention may also be applied to cold working steel. BACKGROUND ART High levels of chromium, molybdenum and/or tungsten and vanadium impart on high speed steels a considerable resistance to * tempering, this being the basic factor responsible for the excellent properties of these steels in cutting tools. These chemical elements also contribute tα the high abrasion resistance of these steels, by combining with carbon in the • steel to form carbides. Conventional manufacture of high speed steel by ingot moulding results in the formation during cooling of course carbide eutectics. These eutectics during the continued working of the hot steel give rise to carbide striation, i e the carbides aggregate in bands or striae. This carbide striation in turn reduces the material strength. In powder metallurgical production of non-porous high speed steel, metal powder which has been allowed to solidify quickly is compacted at a high pressure and a high temperature to full density. In such a material, the carbides become evenly distri- buted, i e not aggregated in bands or striae. Provided the steel does not contain pores, the material strength of high speed steel manufactured according to powder metallurgical methods is therefore much greater than that of conventionally manu¬ factured high speed steel. In order that the steel be completely non-porous, the powder body must be consolidated into a fully dense body by a technique involving the deformation of the individual powder granules so that they fill all cavities. Among such techniques are hot isostatic compaction, pseudo hot iso- static compaction (wherein another powder is used as a pressure transfer medium), forging, and extrusion. A result of the fast sol dification of the metal melt during the manufacture of the powder, is that the carbides in the material to be compacted become very small, their greatest extension normally being no more than 2 j_m. It has long been maintained that a small carbide size in the finished material is really a prerequisite for the high ductility of the high speed steel manufactured by powder metallurgical methods. Therefore, an effort has been made to keep the carbide size down, to be precise to keep it at a level below 3 , in spite of the fact that a course carbide structure makes the steel more abrasion- resistant, a property likewise of primary ' importance to high speed steel . Depending on the area of application, good grindability is also a property aimed at for high speed steel and cold working steel. This property is lso considered to deteriorate if the carbides grow.to a size exceeding 3 pi during the solidification of the steel . These considerations having been foremost, the heating of the steel in connection with the consolidation of the steel has up till now been carried out at a temperature not exceeding approximately 1150*C in order that the formation of carbides greater than 3 jjm be avoided, since higher temperatures cause the carbides to grow considerably faster in high speed steels and cold working steels. DISCLOSURE OF THE INVENTION The invention is based on the observation that the resistance to abrasion of certain powder metallurgically manufactured high speed steels under certain conditions may be favourably influenced without the concurrent loss of material strength. These observations also in dicate that this effect in principle should be obtainable with any type of powder metallurgically manufactured high speed steel, irrespective of its composition with regard to alloying elements, and also with cold working steels. The condition is that the carbide structure of the consolidated, finished steel meet certain criteria, namely: a) At least 40% of the carbides in a randomly chosen section should be > 1.5 μm as measured across their greatest extension. b) At least 25% of the carbide area of a randomly chosen section should be contributed by carbides > 3 urn. c) The largest carbide or carbide aggregate, i e the mean value of the largest extension of the thirty largest carbides and/or carbide aggregates within a randomly chosen area of the steel of 0.29 mπ should be no g 3 reater than Lmax u"rn, as determined by the following expression, D being the diameter or least cross measure, in mm: L max = 10 + !<D 'D -- D being - 50 m ~ L maχ = 18 + * 0 (D - 50), 50 <_ D <_ 100 mm L maχ = 21 p, D being > 100 mm Carbide aggregates in this context signify assemblies of carbides greater than 1 μm, the distance between adjacent carbides being less than the greatest circumscribed radius of the largest of the assembled carbides. Normally, the greatest carbide or carbide aggregate as defined above is no less than 4 μm, preferably no less than 5 μm. To provide the steel with the desired abrasion resistance, the total amount of carbides in the steel must also suffice, this condition being met if the steel contains at least 0.7% carbon and at least 10% of such metals as form carbides with the carbon in the steel, viz chromium, tungsten, molybdenum, and vanadium, or mixtures of these. Apart from these carbide formers other carbide formers may also be part of the alloy, such as titanium, niobium, . tantalum, zirconium, etc. In order that the finished product have a carbide structure in accordance with the above conditions a) - c) a couple of further conditions must also be met, preferably. Firstly, the starting material should be a powder which has been solidified quickly, the microstructure of which should contain no carbides greater than 1 μm as measured across their longest extension, after having been soft annealed at 850°C for 2 h. (The carbide size is measured after annealing for reasons of measurement technique; the values then become reproducible. This does not imply that the annealing procedure necessarily must be part of the manu¬ facturing process of the product according to the invention.) The desired carbide structure of the starting material may be obtained by the use of a gas-atomized powder, the maximum particle size of which is such that the powder passes through a sieve with a mesh size of 1.0 mm, preferably even 0.8 mm mesh. This particle size may be obtained by the adjustment of the atomization of the steel melt, so that only very small drops form, and/or by sieve rejection of courser granules. Another way of obtaining a powder with a carbide structure after annealing at 850°G for 2 h such that it does not contain carbides > 1 μm is to freeze the melt drops extremely quickly, such as by water atomization. In this case however, the powder suffers oxidation, which is a drawback, and hence gas atomization by inert gas is to be preferred. In this connection it may be pointed out that powder which has been gas atomized in the normal way and not sieved contains grains, which after annealing at 850°C for 2 h have a microstructure with carbides normally of a size in the range of 0.5 - 2 μm (see article in Metallovedenie i Terrnicheskaya Obrabotka Metallov, No 10, pp 6 - 8, October 1982; translation published in 1983 by Plenum Publishing Corp.) The second condition is that the material during consolidation or thereafter has been kept at a temperature exceeding 1150*C for a sufficient time to let the initially small carbides grow and transform so that the conditions a) - c) are met. As a result of the fine initial structure, this can be accomplished without the aggregation of carbides, which would occur, did the initial material conta.iπ single carbides of significantly greater size than the rest of the carbides. This latter state occurs if the powder contains grains of considerably greater size than the said sieve mesh size. These larger carbides will act as.growth centres for the formation of single very large carbides or of carbide * aggregates during the high temperature treatment of the steel called for according to the invention. This effect thus may be avoided by the choice of starting material . According to condition c) the carbides must not be larger than a certain measure L maχ , as defined above, since the mechanics of linear elastic fracture teach that the material strength of high speed steels is inversely proportional to the square root of the defect size. It is the largest defect in the volume examined that determines the material strength thereof. For example, the breaking strength of a round bar with a diameter of 100 mm of the known high speed steel ASP 23 as measured transversely is 3.5 kN/mm 2 . On account of the relation of the material strength to the carbide size distribution of high speed steel, the present invention puts the upper limit for the carbide size in the steel at 15 μm, as defined above, preferably at μm, so as to achieve the same material strength and ductility as the known powder metallurgically manufactured high speed steels. These limits also apply to the cold working steels according to the invention. As was stated above, the principles of the invention should be applicable to all alloy compositions of high speed steels, provided the steel contains a sufficient amount, of carbon and carbide-forming metals. This implies that a high speed steel in accordance with the invention should be composed as follows (percentages by weight): C 0.7 - 2.5 Si 0 - 2 n 0 - 2 Cr 2 - 6 . W+2Mo 0 - ' 30 V 0.5 - 7 N traces - 2.5 -Co 0 - 15 The sum Cr + Mo + W + V should not be less than 10%, however. Further, the steel may contain other alloying elements, accessory elements and impurities in normal amounts, the balance being iron. Cold working steels according to the invention should be composed as follows (percentages by weight): c 1 - 3. 5 Si 0.1 - 2 Mn 0.1 - 2 N traces - 0. 5 Cr 10 - 18 +2Mo traces - 5 V 0 _. 10 , the balance being essentially iron, impurities, and accesory elements in normal concentrations. Within the scope of the invention are also high speed steels and cold working steels with good grindability in spite of the presence of large carbides in the steel. This aspect of the invention is based on the observation that the grindability of high speed steels is impaired mainly by the large carbides of the MC type, whereas the M fe C-carbides are considerably less harmful in this respect. For applications where the grindability of the steel is of prime importance, this obser¬ vation may be utilized for steels according to the invention by choosing such an alloy composition that the MC content is minimized, the amount of M^C-carbides formed instead being increased as compared to known high speed steels. In particular, the vanadium content of the steel in accordance with this aspect of the invention has been adjusted in such a way that essen¬ tially all the vanadium of the steel is either dissolved in the matrix or mixed with molybdenum and tungsten in the M 6 C-carbides This steel is also kept, during the consolidation of the metal powder to a fully dense body, at a temperature in excess of what has previously been possible for powder steel, which allows the hard particles, essentially M fe C-carbides, to grow to the sizes mentioned above, said sizes previously having been unacceptable for known easily grindable powder steels. When manufacturing cold working steels containing vanadium by powder metallurgical methods, the formation of MC-carbides may be inhibited corres¬ pondingly, favouring instead the formation of larger M,C 3 - carbides. An easily grindable cold working steel according to the invention thus is characterized by the fact that its content of hard phases essentially consists of M ? C 3 -carbides. In case the invention relates to a high speed steel of good grindability, the vanadium content should, in order that large MC-carbides in the steel be avoided, be selected so that the following condition is met: 0.1 + 0.05(2Mo + W)% < V < 0.8 + 0.05(2Mo + W)% , and the carbon content should meet the following condition: 0.25 + 0.03(2Mo + W)% < C < 0.45 + 0.03(2Mo + W)% . The cold working steel according to the invention should have a vanadium content such that -2.4 + 0.1(3.5Cr + 2Mo + W) < V. < -1.6 + 0.1(3.5Cr + 2Mo + W) and a carbon content such that -1.3 + 0.07(3.5Cr + 2Mo + W) < C < -0.9 + 0.07(3.5Cr + 2Mo + W) Further characteristics, aspects, and advantages of the invention will become apparent from the following examples and experimental results. DESCRIPTION OF DRAWINGS The drawing attached is a diagram with a pair of curves 1 and 2. The curve 1 illustrates the breaking strength of a known non-porous high speed steel manufactured powder metallurgically, as a function of the diameter of the product. In this case, the products were rounds. This known high speed steel had carbides of a maximum extension of 3 μm and had been manufactured by consolidation at a temperature of maximally 1150*C of a powder containing, after annealing at 850 β C for 2 h, carbides of sizes in the range 0.5 - 2 μm. The breaking strength values were determined after hardening from 1180°C in 3 min and tempering at 560 β C for 3 x 1 h. The second curve 2 illustrates the mean value of the maximum extensions of the 30 largest carbides and/or carbide aggregates which may be accepted in a steel according to the invention within a randomly chosen area of 0.29 mm* if the same breaking strength is to be obtained as that of the known high speed steel corresponding to curve 1. The curve 2 has been derived theoretically on the basis of linear elastic fracture theory, which teaches that the material strength of high speed steel is inversely proportional to the square root of the size of the largest defect in the steel, but has also been verified empi¬ rically. The curve 2 may be approximated by three straight line sections 3, 4, and 5, for the dimension intervals D < 50 mm, 50 mm < D < 100 mm, and D > 100 mm, respectively. These three straight line sections 3, 4, and 5 form the basis for the algorithms of condition a) on page 3. - EXAMPLES The steels listed in Table 1 have been examined. All concentration values are nominal percentages by weight. TABLE 1 Steel No C Si Mn Cr Mo W Co V S Type 1 High Speed Steel 1.28 0.5 0.3 4.2 5.0 6.4 - 3.1 n.a. (ASP 23) 2 High Speed Steel 1.15 0.5 0.5 4.2 6.5 6.0 - 2.1 0.1 3 High Speed Steel 0.95 0.5 0.5 4.2 6.8 6.0 - 1.3 0.1 (ASP 24) 4 High Speed Steel 1.28 0.5 0.3 4.2 5.0 6.4 8.5 3.1 n.a. (ASP 30) 5 High Speed Steel 0.95 0.5 0.5 4.2 6.8 6.0 8.5 1.3 0.1 (ASP 31) 6 Cold Working Steel 2.0 0.5 0.3 12 1 2.2 n.a. 7 Col d Worki ng Steel 2.7 0.5 0.3 15 1 3.2 n . a. 8 Cold Working Steel (M2) 0.8 0.25 0.25 4 5 6.2 - 1.9 n . a. n . a. = not analyzed STARTING MATERIAL The starting material was tool steel powder produced by gas atomization of a steel melt according to the technique described in US-A-3813 196. The atomization gas was nitrogen. The powder was sieved to the desired size. The M2 sample, steel No 8, was produced by conventional ingot moulding and forging. CONSOLIDATION - STRUCTURAL TREATMENT The powder was filled into steel sheet capsules which were then evacuated and sealed. Certain of the capsules were heated and subjected to hot isostatic compaction to full density according to prior art at about 1150°C, whereas other capsules were heated to 1210°C. The capsules were hot worked according to the art to final dimensions and soft annealed. Sample bars were cut and hardened from 1180°C and tempered at 560°, 3 times for 1 h each time, except for steel No 8, which was hardened from 1220 β C and tempered at 560°.C, 2 x 1 h. RESULTS Structure and properties were examined and the results are presented in Table 2. The maximum carbide size was determined in accordance with the definition given in the preceding part of - this description, viz the mean value of the largest extension of the 30 largest carbides and/or carbide aggregates of the steel within a randomly chosen area of 0.29 mm 1 . The grindability was determined by a method presented in the Jernkontorets Annaler 153, 1969, pp 583 - 589. The material strength was determined by the four-point bending test, transversely to the sample extension. The properties of the cold working steels have not been evaluated. TABLE 2 Steel Sample Structural heat Final Carbides Carbide Maximum No No treatment, product >1.5 μm, area carbide °C/h diameter % of all contri¬ size after carbides buted accord¬ forging/ by ing to rolling carbides defini¬ 0 mm >3 μm, tion % of c) , μm total carbide area 1 1A 1150/3h 92 15 3 1 IB 1210/48h 100 43 10 2 2 1210/48h 100 73 6.5 3 3A 1210/72h 112 65 63 7.S 3 3B 1150/3h 100 3 3 3C 1210/72h 7.5 43 26 6.7 4 4A 1150/3h 100 16 2 3 4 4B 1210/3h 100 4 4C 1150/3h 6 16 3 Δ. 4D 1150-1200/120h 6 16 4 4E 1210/72h 7.5 58 32 6.8 5 5A 1210/72h 112 63 57 7.6 5 5B 1150/3h 100 3 8 8A - - 150 14 45 15 8 8B _ 25 24 24 c) The maximum carbide size is the mean value of the largest extensions of the 30 largest carbides or carbide aggregates within a randomly chosen area of 0.29 mm. 2 13 TABLE 2 (contd) Steel Sample Total Bending Grind¬ Hardness, No No carbide strength ability, HRC amount, L=longitud. min % by vol. T=transv. , kN/mm 1 1A 13 3.5T 9 65 1 IB 13 3.5T 1.5 65 2 2 13 3.5T 2.8 65 3 3A 13 4.7L 6.8 65 3.5T * _ 3 3B 13 3.5T 65 5 3 3C 13 3.5T 65 4 4A 13 3.2T 8 66 4 4B 13 3.2T 4 4C 13 5.1L * 4 4D 13 4.4L 66 0 4 4E 13 66 5 5A 13 3.2T 4.8 66 5 5B 13 3.2T 66 .. . 8 8A 9 1.5T 65 8 8B 9 3.2T ' 65 ς 4.5L 0 5 Steel No 1 contained both M 6 C-carbides and MC-carbides. The respective carbide volumes are as follows, irrespective of heat treatment. TABLE 3 Steel No M 6 C MC Total % by vol. % by vol . % by vol . , . appr 1 8 5 13 3 13 <0.5 13 The total amount of V present in steel No 3 was 1.3%. The matrix contained about 1% V and the rest, about 0.3%,was associated with mainly Mo and W in the M fc C-carbides. The total amount of MC-carbides was negligible.

Claims: CLAIMS 1. Tool steel, comprising high speed steel and cold working steel, produced from metal powder by compaction at a high pressure and a high temperature to full density, c h a r a c t e r i z e d i n that a) at least 40 % of the carbides of a randomly chosen section have a largest extension > 1.5 μm, b) at least 25 % of the carbide area of a randomly chosen section is contributed by carbides with an extension > 3 μm, c) the steel contains carbides, the maximum size L__ v of which, i e the mean value of the largest extensions of the thirty largest carbides and/or carbide aggregates within a randomly chosen area of a section of the steel of 0.29 mm , meets the following conditions, where D is the diameter or smallest gauge of the product: L = 10 +S-. • D-, D being < 50 mm ' max 3ϋ — L = 18 +3_ (D - 50), for 50 < D < 100 mm max 50 — — Lmax= 21 rμm, D being- *■ > 100 mm, carbide aggregates in this context meaning those collections of carbides larger than 1 μm in which the distance between adjacent carbides is less than the greatest circumscribed radius of the largest of the proximal carbides, and that d) the steel contains at least 0.7 % carbon and at least 10 % of one or several of the following metals: chromium, tungsten, molybdenum, and vanadium, or mixtures of these. 2. Tool steel according to claim 1, c h a r a c t e r i z e d n that it is produced from a powder, the microstructure of said powder after heating at 850°C for 2 h containing carbides with a maximum extension of 1 μm. 3. Tool steel according to claim 1, c h a r a c t e i z e d i n that the maximum carbide size as defined in claim 1 is at least 4 μm. 4. Tool steel according to claim 3, c h a r a c t e r i z e d i n that the maximum carbide size is at least 5 μm. 5. Tool steel according to any of the claims 2 - 4, c h a r a c t e r i z e d i n that it has been heat treated, during or after consolidation, at a temperature in excess of 1150°C, preferably in excess of 1200°C, for a time sufficient to permit the carbides of the starting material to grow enough to meet the said conditions for the carbide structure of the finished product. 6. Tool steel according to any of the claims 1 - 5, c h a r a c t e r i z e d i n that the starting material is-a gas atomized powder with a maximum powder grain size permitting the powder to pass through a sieve, the mesh size of which is 1.0 mm, preferably permitting the powder to pass through a sieve with the mesh size 0.8 mm. 7. Tool steel according to any of the claims 1 - 6, c h a r a c t e r i z e d i n that it is a high speed steel with the following composition in percentages by weight: C 0.7 - 2.5 Si 0 - 2 Mn 0 - 2 Cr 2 - 6 W+2Mo 0 - 30 V 0.5 - 7 N traces - 2.5 Co 0 - 15 , the sum of the percentages for Cr, Mo, W, and V however being at least 10, the balance being essentially only iron, accessory elements, and impurities in normal amounts. 8. High speed steel according to claim 7, c h a r a c t e r i z e d i n that it essentially consists of Si 0.1 - 2 Mn 0.1 - 2 N traces - 0.5 Cr 3 - 6 Co 0 - 13 2Mo+W 10 - 22 , an amount of V such that 0. 1 + 0.05(2Mo + W)% < V < 0.8 + 0, .05(2Mo + W)% , an amount of C such that 0.25 + 0.03(2Mo + W)% < C < 0.45 + 0.03(2Mo + W)% , the balance being essentially iron, impurities and accessory * elements in normal amounts, and that the steel contains 5 - 16 % by volume of hard phase, said hard phase consisting of M β C- carbides with an effective maximum carbide size as defined in claim 1 lying between 4 and 15 μm. 9. High speed steel according to claim 8, c h a r a c e r i z e d i n that it contains 16 - 20 % of (2Mo + W). 10. High speed steel according to claim 8, c h a r a c t e r i z e d i n that the vanadium and carbon contents are such that 0.2 + 0.05(2Mo + W)% < V < 0.5 + 0.045(2Mo + W)% and 0.29 + 0.03(2Mo + W)% < C < 0.4 + 0.03(2Mo + W)% . 11. Steel according to claim 10, c h a r a c t e r i z e d i n that the vanadium content expressed in percent by weight is 0.34 +/- 0.1 + 0.045(2Mo + W)% and that the carbon content expressed in percent by weight is nominally 0.36 +/- 0.02 + 0.03(2Mo + W)% . 12. Tool steel according to claim 8, c h a r a c t e r i z e d i n that i contains 3 - 5 % Cr, 6 - 7 % Mo, and 5 - 7 % W. 13. Tool steel according to any of claims 1 - 7, c h a r a c t e r i z e d i n that it is a cold working steel of essentially the following composition: Si 0.1 - 2 Mn 0.1. - 2 N traces - 0.5 Cr 10 18 2Mo+W traces - 5, a vanadium content such that -2.4 + 0.1(3.5Cr + 2Mo + W) < V < -1.6 + 0.1(3.5Cr + 2Mo + W) , a carbon content such that -1.3 + 0.07(3.5Cr + 2Mo + W) < C < -0.9 + 0.07(3.5Cr + 2Mo + W), the balance being iron, impurities, and accessory elements in normal amounts, and that the steel contains 10 - 40 % hard phase, said hard phase essentially consisting of M^-carbides.

Inventors: HELLMAN PER, WISELL HENRY, HELLMAN, PER, WISELL, HENRY
Applicants: KLOSTER SPEEDSTEEL AB, KLOSTER SPEEDSTEEL AKTIEBOLAG
Application year: 1986
Main classification: C22C33
IPC codes: B22F3, C22C33