THERMAL SHOCK RESISTANT TITANIUM BASED CARBONITRIDE AND SINTERING METHOD TO MANUFACTURE IT

Abstract: According to the present invention a titanium based carbonitride cutting tool insert with superior thermal shock resistance is provided. This is accomplished by sintering the material under conditions where the melting process is reversed. The melt forms in the centre of the material first and the melting front propagates outwards towards the surface. This leads to minimal porosity and a macroscopic cobalt depletion towards the surface. The cobalt depletion, in turn, leads to a favourable compressive residual stress in the surface zone.

Description: Thermal shock resistant titanium based carboni tr ide and sintering method to manufacture it. The present invention relates to a liquid phase sintered body of a carbonitride alloy with titanium as main component which has improved properties particularly when used as cutting tool material in cutting operations requiring high thermal shock resistance. These improved properties have been achieved by processing the material in a specific way to obtain a lower melting point of the liquid phase in the interior of the body compared to the surface. In this way porosity and residual oxygen content is minimised and, in addition, a binder phase gradient leading to a beneficial compressive residual stress in the surface zone can be produced. Titanium based carbonitride alloys, so called cermets, are today well established as insert material in the metal cutting industry and are especially used for finishing. They consist of carbonitride hard constituents embedded in a metallic binder phase. The hard constituent grains generally have a complex structure with a core surrounded by a rim of other composition. In addition to titanium, group Via elements, normally both molybdenum and tungsten and sometimes chromium, are added to facilitate wetting between binder phase and hard constituents and to strengthen the binder by means of solution hardening. Group IVa and/or Va elements, i.e. Zr, Hf, V, Nb and Ta, are also added in all commercial alloys available today. All these additional elements are usually added as carbides, nitrides and/or carbonitrides . The grain size of the hard constituents is usually <2 μm. The binder phase is normally a solid solution of mainly both cobalt and nickel. The amount of binder phase is generally 3 - 25 wt% . Other elements are sometimes added as well, e.g. aluminium, which are said to harden the binder phase and/or improve the wetting between hard constituents and binder phase . Despite more than 20 years of intense development efforts world-wide, it has not been possible to increase the rather narrow application area of cermets. It is still limited to finishing or at most semi-finishing operations requiring moderate wear resistance and toughness. US patent 4,985,070 discloses a process for producing a high strength cermet. This is accomplished by sintering the material in progressively increasing nitrogen partial pressure to eliminate denitrification and obtain better control of the final nitrogen content. This is useful to obtain improved process control during conventional sintering especially of cermets with extremely high nitrogen content. Unfortunately it also eliminates the possibility to produce different melting points in different parts of the material, the process utilised in the present invention. Through WO 96/22403 and WO 97/04143 the limited wear resistance of cermets has been overcome and a significant step forward has been taken towards tougher material. This is accomplished by optimising the raw material compositions and by applying CVD coatings onto suitable cermet alloys to obtain compressive residual stresses in the coating which increase toughness. In both cases conventional sintering technique is used. However, further steps toward improved toughness, in particular improved thermal shock resistance, need to be taken to compete with CVD-coated WC-Co based alloys in many toughness demanding applications. When doing so, is most probably necessary to find novel processing methods. Continued optimisation mainly of chemical composition and raw material compositions is not likely to have the desired effect. It is an object of the present invention to provide a sintered titanium based carbonitride alloy, having minimum porosity and oxygen content, and a compressive residual stress in the surface zone, both leading to significantly improved thermal shock resistance, and a method for producing such alloys. Fig 1 shows an EPMA (Electron Microprobe Analysis) line scan analysis of Co, N, W and C through one side of an insert of the present invention. Fig 2 also shows an EPMA line scan analysis of Co, N, W and C through one side of an insert of the present invention . Fig 3 shows an EPMA line scan analysis of Co, N, W and C through one side of a comparative insert. The sintered titanium-based carbonitride alloy of the present invention contains 2-15 atomic %, preferably 2-6 atomic % , tungsten and/or molybdenum. Apart from titanium, the alloy contains 0-15 atomic % of group IVa and/or group Va elements, preferably 0-5 atomic % tantalum and/or niobium. As binder phase forming element 5-25 atomic % , preferably 9-16 atomic % , cobalt is added. The alloy has a N/ (C+N) ratio in the range 10-60 atomic %, preferably 25-51 atomic %. The alloy must not contain nickel and/or iron apart from inevitable impurities. If these binder forming elements are included, the novel process reverts to a conventional one and the desired microstructure cannot be produced. Most preferably no elements apart from C, N, Ti, W, Ta and Co are intentionally added. In a first preferred embodiment useful for toughness demanding applications requiring relatively low plastic deformation resistance the composition is 3-5 atomic % W, 10.5-14 atomic % Co, 25-50% N/ (C+N) , balance Ti . In a second preferred embodiment useful for applications requiring relatively high plastic deformation resistance the composition is 3-5 atomic % W, 6-14 atomic %, preferably 10.5-14 atomic % Co, 25-50% N/(C+N), 1-4 atomic % Ta, balance Ti . In a third preferred embodiment useful for applications requiring especially high thermal shock resistance the composition is 75-90% Co in the surface compared to centre . In a fourth embodiment the composition is 95-99% Co in the surface compared to centre. This is useful e.g. for special insert geometries requiring grinding so that only the positive effect of the reversed melting direction but not the cobalt gradient itself can be utilised. The microstructure is characteristic for an alloy which has melted from the centre and outwards towards the surface, i.e. where shrinkage due to pore elimination starts in the centre and propagates outwards. Porosity and residual oxygen content is minimized, porosity class A02 or less and an oxygen content below 0.8, preferably below 0.5, atomic% and a macroscopic, essentially parabolic cobalt gradient exists where the cobalt content decreases monotonously, apart from normal statistical fluctuations, from the centre of the alloy to the surface. The average cobalt content as measured in a zone 0-9 μ below the surface is 50-99%, preferably 75-99%, most preferably 75-97.5%, of the cobalt content in the centre of the alloy. This gradient leads to a monotonously increasing compressive residual stress in the hard phase skeleton from the centre towards the surface. The alloy may be coated with at least one wear resistant coating, preferably using the techniques described in WO 97/04143. This alloy has superior thermal shock resistance and is suitable as a cutting tool material. In another aspect of the invention, there is provided a method of manufacturing a sintered carbonitride alloy in which powders of carbides, carbonitrides and/or nitrides are mixed with cobalt to a prescribed composition and pressed into green bodies of desired shape. The green bodies are liquid phase sintered in vacuum or a controlled gas atmosphere at a temperature in the range 1370-1500 °C, depending on composition. In the heating part of the sintering cycle, before the maximum temperature is reached, a desoxidation and denitrification step is included which gives the alloy its superior properties. Due to the design of this step the liquid binder phase nucleates in the centre of the alloy first. The melting front then propagates outwards towards the surface. During normal liquid phase sintering, melting starts at the surface and propagates inwards, towards the centre. Reversing the melting direction has two desirable effects: Any residual gas is pushed out from the green body instead of being trapped when the porosity is closed. In this way residual porosity in the sintered alloy is minimized, leading to higher strength. Secondly, as the melting front moves through the alloy the capillary forces of the molten binder produce the macroscopic cobalt gradient described above. This gradient is stable through the remainder of the sintering process and its magnitude can be controlled with good accuracy. At temperatures above about 900 °C desoxidation of the surface of individual Ti-containing hard phase grains occurs, as oxygen originating from these surfaces leaves the green bodies in the form of carbon monoxide gas (CO) . In this way, carbon is taken predominantly from the same surface, thus decreasing the stoichiometry of the surface. At temperatures above about 1250 °C denitrification of the surface of individual nitrogen containing hard phase grains occurs as nitrogen originating from these surfaces leaves the green bodies in the form of nitrogen gas (N2) • Denitrification also decreases the stoichiometry of the surface. The relative efficiency of the two processes determines the C/N ratio of the surface. The oxygen and nitrogen content on the surface is determined by the temperature and the partial pressures of CO and N2 , respectively, outside the surface. Increasing the temperature or decreasing the partial pressures will decrease the O- and/or N-content on the surface. It has quite surprisingly turned out that, for the compositions specified above, the desoxidation and denitrification processes described above can be utilised to obtain a substantially lower melting point in the centre of the green body compared to the surface. This is achieved by an appropriate combination of temperature ramp and CO- and N2 partial pressures in the furnace in the temperature interval between 900 °C and until a liquid binder has formed throughout the material (normally in the range 1350-1430 °C depending on composition) . The reason for this has turned out to be that gas transport through the open porosity of the green bodies is a much slower process than was previously thought. Due to this it is possible to maintain significant CO- and/or N2 pressure gradients through the green body, with highest pressures in the centre and lowest at the surface. The magnitude of these gradients are controlled by the rate of gas formation inside the green body, the average pore size through which gas transport occurs and the partial pressures at the surface of the green body. The rate of gas formation depends on the C/N ratio in the alloy, the stoichiometry of the raw material and the degree of surface oxidation of the raw material grains . By keeping these parameters constant the rate of gas formation can be controlled by the slope of the temperature ramp. A steeper ramp leads to a higher rate of gas formation. The average pore size increases with increasing grain size and decreasing compaction pressure when pressing the green bodies. The partial pressures of CO- and N2~gas at the green body surface is controlled by the vacuum pump capacity or by using a controlled furnace atmosphere, either as stationary gas or as flowing gas. Stationary gas may originate from the green bodies themselves or be added from an external source. Hard phase grains situated at a given depth from the green body surface will obtain a surface stoichiometry and/or surface C/N ratio determined by the CO and N2 pressure in the open porosity at that depth. Increased stoichiometry and/or C/N ratio leads to decreased melting point. Thus, the lowest melting point will be obtained in the centre of the green body where the CO and N2 pressures are highest. A large difference in melting point between green body surface and centre leads to a large cobalt gradient. Since the parameters governing the pressure gradient through the green body, and thus the difference in melting point obtained, are intimately connected, the appropriate combination of conditions must be determined experimentally. However, in the most critical temperature interval, between 1300 °C and that temperature at which a fully molten binder exists (normally about 1400 °C) , the temperature increment should lie in the range 0.5-15 °C/minute, but can be interrupted with optional temperature plateaux when needed e.g. to pump away excessive gas originating from the green bodies . During the same temperature interval the CO- and N2 partial pressures should be kept below 20 mbar, preferably below 15 mbar CO and most preferably below 5 mbar N2. in order not to reverse the pressure gradients and initiate the melting process at the surface (A thin molten surface zone that essentially does not propagate inwards is acceptable. Such a zone may be obtained due to radiation heating and will not lead to pore closure as long as it is sufficiently thin) . Since the process is controlled by reactive gases in the sintering atmosphere, it is a definite advantage to place the green bodies on a surface which is inert to this atmosphere. One good example of this is yttria coated graphite trays, as described in WO 97/40203. Using zirconia or graphite in contact with the green bodies has in some cases led to an asymmetric cobalt gradient from top to bottom of the insert. This is unacceptable since the performance will vary between different cutting edges on the insert. Example 1 A powder mixture with a chemical composition of (atomic%) 40.7% Ti, 3.6% W, 30.4% C, 13.9% N and 11.4% Co was manufactured from Ti(C,N), WC and Co raw material powders. The mean grain size of the Ti(C,N) and WC powders were 1.4 μ . The powder mixture was wet milled, dried and pressed into green bodies of the insert type CNMG 120408-PM at a compaction pressure of 130 MPa. The green bodies were dewaxed in H2 at a temperature below 350 °C. The furnace was then evacuated and pumping was maintained throughout the temperature interval 350-1430 °C. From 350-1200 °C a temperature ramp of 10 °C/minute was used. The temperature was then held at 1200 °C for 30 minutes to pump out excessive gas originating from the inserts. A temperature ramp of 4 °C/minute was then applied in the interval 1200-1430 °C . The sum of the CO- and N2 partial pressures was about constant at 0.01 mbar from 1300 °C until 1430 °C when the open porosity was closed (i.e. the melting front had reached the surface) and the pressure had decreased somewhat. The inserts were liquid phase sintered at 1430 °C for 90 minutes in a 10 mbar Ar atmosphere. Polished cross sections of the inserts were prepared by standard metallographic techniques and characterised using optical microscopy and electron microprobe analysis (EMPA) . Optical microscopy showed that the inserts were free from residual pores (porosity class A00) . Figure 1 shows an EMPA line scan analysis of Co, N, W and C ranging from one side of the insert, through the interior of the material and to the opposite surface. Clearly, the cobalt content decreases monotonously from the centre towards the surface, while the concentration of the other elements is fairly constant across the insert. At the surface the cobalt content is about 87% of that in the centre. Example 2 In a second experiment, inserts were manufactured in an identical manner as described in example 1 except that the valve to the vacuum pump was kept closed in the temperature interval 1300-1430 °C . During this interval the temperature increment was lowered to 3 °C/minute. The sum of the CO- and N2 partial pressures increased linearly from about 0.01 mbar at 1300 °C to about 6 mbar at 1360 °C when the open porosity was closed and the pressure stopped increasing. Figure 2 shows an EMPA line scan analysis of this material, obtained under identical conditions as in example 1. Again, the cobalt content decreases monotonously from the centre towards the surface, while the concentration of the other elements is fairly constant across the insert. At the surface the cobalt content is about 95% of that in the centre. The slower temperature ramp, in combination with the higher partial pressures of CO- and N2 gas in the furnace have decreased the magnitude of the cobalt gradient consi- derably. Optical microscopy showed that the inserts were free from residual pores (porosity class A00) . Example 3 In a third experiment, inserts of the geometry SNUN120408 were manufactured in an identical manner as described in example 1 except that in three separate runs the sintering cycle was stopped at 1200°C after the 30 minute plateau, at 1350 °C and at 1400 °C respectively. The furnace was allowed to cool down and the inserts from the different runs were inspected. Characteristic for this insert geometry is that all six sides of both unsintered and fully sintered insert are flat. Inspection of the inserts from the three interrupted runs showed that at 1200 °C the inserts had shrunk linearly about 5% compared to the dimensions of the unsintered green body. All sides were completely flat. This amount of shrinkage is expected to be obtained from solid state sintering, a process occurring before any liquid phase has formed. At 1350 °C the inserts had shrunk 11%. Now all six sides were visibly concave, clear evidence that shrinkage due to liquid formation has started in the centre of the insert. At 1400 °C the inserts had nearly reached their fully sintered dimensions (18% linear shrinkage compared to the green body) . All sides were markedly concave showing that the melting front had not yet reached the outermost edges of the insert. For an insert melting in the opposite direction the sides are expected to stay flat or possibly convex during shrinkage. Example 4 In a fourth experiment, inserts were manufactured in an identical manner as described in example 2 except that in the temperature interval 1300-1430 °C a gas mixture of 10% N2 and 90% CO was allowed to flow through the furnace. Simultaneously, the pumping capacity was adjusted to simulate the pressure increment obtained in example 2. EMPA line scan analysis of the material, showed an identical Co-profile as obtained in example 2. This is clear evidence that it is in fact the N 2 and CO partial pressures that determine the structure since all other gases have very low partial pressures when the experiment is performed in this manner. Example 5 (Comparative) In a fifth experiment, inserts were manufactured in an identical manner as described in example 4 except that in the temperature interval 1300-1430 °C the pumping capacity was adjusted to obtain a faster pressure increment compared to example 4. The pressure was allowed to increase to 20 mB at 1430 °C . EMPA line scan analysis of the material, showed a complete absence of Co-profile. Optical microscopy showed a large core region with significant porosity (A06) , while the surface zone was essentially pore free (A00) . Furthermore, this material showed an increase in magnetic saturation of about 15% compared to the material of example 4, indicating a higher carbon content. Chemical analysis showed that both the carbon and oxygen content was about 0.2 wt% higher for this material compared to example 4. The result obtained is strong evidence that the porosity is closed from the surface and that (predominantly) CO gas is trapped in the material. Example 6 (Comparative) As a reference, CNMG120408-PM inserts were manufactured of a powder mixture consisting of (in atomic-%) 8.3 Co, 4.25 Ni , 43.8 Ti, 2.5 Ta, 0.8 Nb, 4.2 W, 2 Mo, 26.6 C and 16.6 N using an identical sintering process as in example 1. These inserts were coated with an about 4 μ thick Ti (C,N) -layer and a less than 1 μm thick TiN-layer using the physical vapour deposition technique (PVD) . This is a well established PVD-coated cermet grade within the P25-range for turning and is characterised in particular by good toughness. Figure 3 shows an EMPA line scan analysis of this material obtained under identical conditions as in example 1. This material does not have a Co-gradient, in spite of a sintering process that gave a large gradient for the composition used in example 1. The reason is the large amount of nickel used in this material. Light optical microscopy showed that this material has normal residual porosity (porosity class A02) . Example 7 In order to test the toughness of the material in example 1, inserts were both PVD coated (insert A), using the same process as in example 4, and CVD coated (insert B) using a thick coating consisting of 10 μm Ti(C,N) and 5 μm AI2O3. The thin PVD coating can be expected to have only marginal effect on the toughness of the insert, while the CVD coating, due to its thickness, can be expected to decrease the toughness dramatically. The thermal shock resistance of the inserts was tested in a facing operation with cutting fluid, using a cylindrical bar of SS2511 steel as workpiece material. Inserts from example 4 were used as reference (insert C) . Thermal cycling was obtained by performing each facing pass as a sequence of nine separate cuts where the cutting fluid was allowed to cool the cutting edge between each individual cut. Tool life criterion was edge fracture or 30 full passes. The number of passes needed to reach end of tool life was measured for each cutting edge and three edges per variant were tested. The speed was 400 m/min, the feed 0.35 mm/revolution and the depth of cut was 2 mm. The result is given in Table 1 below. Table 1 Edge no insert A insert B insert C 1 30.0 8.2 0.2 2 15.4 8.1 0.2 3 25.0 9.0 0.2 average 23.5 8.4 0.2 Comparing the results of inserts A and C, which have identical coating, it is clear that the thermal crack resistance is dramatically improved by the invention. Even with a thick brittle coating, insert B, fractures caused by thermal cycling is delayed considerably.

Claims: Claims 1. A cutting tool insert of sintered titanium-based carbonitride alloy containing hard constituents based on Ti, Zr, Hf, V, Nb, Ta, Cr, Mo and/or W in a cobalt binder phase, c h a r a c t e r i s e d in that said insert has a macroscopic cobalt gradient in which the cobalt content decreases monotonously, apart from normal statistical fluctuations, from the centre of the insert to its surface and reaches a cobalt content in a zone 0- 9 μm below the surface of 50-99% of that in the centre. 2. A cutting tool insert according to any of the previous claims, c h a r a c t e r i s e d in that said insert contains porosity in the class A02 or less. 3. A cutting tool insert according to any of the previous claims c h a r a c t e r i s e d in containing apart from inevitable impurities in addition to titanium, 2-15, preferably 2-7, atomic % tungsten and/or molybdenum, 0-15 atomic % of group IVa and/or group Va elements apart from titanium, tungsten and/or molybdenum, preferably 0-5 atomic % tantalum and/or niobium, 5-25, preferably 9-16, atomic % cobalt and with an average N/ (C+N) ratio in the range 10-60, preferably 25-51, atomic %. 4. A cutting tool insert according to any of the previous claims c h a r a c t e r i s e d in that said insert is provided with at least one wear resistant coating comprising Ti and/or Al . 5. Method of manufacturing by liquid phase sintering a body of titanium based carbonitride alloy, containing hard constituents based on Ti, Zr, Hf, V, Nb, Ta, Cr, Mo and/or W in a cobalt binder phase c h a r a c t e r i s e d in that sintering is performed under such conditions that the liquid binder phase forms in the centre of the body first and the melting front then propagates outwards towards the surface. 6. Method of manufacturing a sintered body according to claim 5, c h a r a c t e r i s e d in that in the temperature range between 1300 °C and until all cobalt has molten the temperature increment lies in the range 0.5-15 °C/min, apart from optional temperature plateaux. 7. Method of manufacturing a sintered body according any of claims 5 or 6, c h a r a c t e r i s e d in that in the temperature interval between 1300 °C and until all cobalt has molten the CO- and N2 partial pressures in the furnace are kept below 20 mbar, preferably below 15 mbar, most preferably below 5 mbar. 8. Method of manufacturing a sintered body according to any of claims 6, 7 or 8 c h a r a c t e r i s e d in that the body contains apart from inevitable impurities in addition to titanium, 2-15, preferably 2-7, atomic % tungsten and/or molybdenum, 0-15 atomic % of group IVa and/or group Va elements apart from titanium, tungsten and/or molybdenum, preferably 0-5 atomic % tantalum and/or niobium, 5-25, preferably 9-16, atomic % cobalt and with an average N/ (C+N) ratio in the range 10-60, preferably 25-51, atomic %. 9. Method of manuf cturing a sintered body according to any of claims 6, 7, 8 or 9 c h a r a c t e r i s e d in that the body is sintered on an yttria surface.

Inventors: LINDAHL PER, ODEN CAMILLA, ROLANDER ULF, WEINL GEROLD, LINDAHL, PER, ODEN, CAMILLA, ROLANDER, ULF, WEINL, GEROLD
Applicants: SANDVIK AB, SANDVIK AB(PUBL)
Application year: 1998
Main classification: C22C29
IPC codes: B22F3, B23B27, C22C1, C22C29