Modeling and Simulation for Material Selection and Mechanical Design Part 11 doc

aged [138]. The results are represented by a continuous curve for each geo- metry (symbols). Each point of a curve represents a location r along the radius in the smallest cross-section. Only one point of each curve fulfills the failure criterion for ductile fracture, so that the envelope of all curves represents the failure criterion. For quasi-static loading (Fig. 67a), the envel- ope is described by the Hancock=M ackenzie relation and for dynamic load- ing (Fig. 67b) by Eq. (111). The comparison between the failure criterions determined for quasi- static and dynamic loading is represented in Fig. 68b in addition to that Figure 67 Local equivalent plastic strain at fracture as a function of the degree of multiaxiality ðs m =s v Þ along the specimen radius at the narrowest cross-section of differently notched specimen of aluminum AA7075 highly over aged under (a) quasi- static, and (b) dynamic loading. (From Ref. 138.) Copyright 2004 by Marcel Dekker, Inc. All Rights Reserved. Figure 69 The transition temperature shift due to an increase in multiaxiality M ¼ s m =  ss, prestrain e and rate of elongation. Figure 70 Influence of deformation rate and strength on the transition temperature shift [141]. (a) J-integral-temperature curves for steel 15NiCuMoNb5. (b) Transition temperature shift as a function of yield strength. (c) Measured and calculated values for the transition temperature as a function of the machine ram velocity v. " Copyright 2004 by Marcel Dekker, Inc. All Rights Reserved. If this is the case, the brittle fracture condition is simply assumed to be s à f À s I ¼ 0. The microscopic cleavage strength s à f can be considered as pro- portional to the modulus of elasticity EðTÞ. The transition temperature T t from brittle to ductile fracture can be determined by the intersection of the functions s à f ðTÞ and  ssðTÞ for given values of multiaxiality M, prestrain e, and strain rate _ ee. A variation of these parameters results in a shift of the transition temperature which is determined by DT ¼ ð@s I =@MÞDM þð@s I =@eÞDe þð@s I =@ _ eeÞD _ ee ðds à f =dTÞÀð@s I =@TÞ ð114Þ where ds à f =dT % dE=dT. However, this equation seems to overestimate the transition temperature shift. An alternative procedure for the determination of the effect of the loading rate on the transition temperature, which describes the experimental results more accurately, was introduced by Falk and Dahl [141]. This procedure needs the knowledge of a single value T t1 for the transition temperature at a known loading rate as well as the relation between flow stress, strain rate, and temperature determined, e.g. in tension tests. According to their analysis, the transition temperature for another strain rate is determined by the intersection of the function mðTÞ and T t1 þ DT=ð@m=@TÞ T¼0 where m ¼ @ ln s=@ ln _ ee is the strain rate sensitivity. According to this method, the transition temperature shift can be expressed by DT ¼ @m @T  T¼0 À @m @T  ! À1 @m @ ln _ ee D ln _ ee ð115Þ Figure 70 shows experimental results determined and their description by Eq. (115). REFERENCES 1. Ludwik, P. Elemente der technologischen Mechanik; Springer-Verlag: Berlin 1909. 2. Hollomon, J.H. Tensile deformation. Trans AIME 1945, 126, 268–290. 3. Swift, M.W. Plastic instability under plane stress. J. Mech. Phys. Solid 1952, 1, 1–18. 4. Voce, E. The relationship between stress and strain for homogenous deformation. J. Inst. Metals 1948, 74, 537–562. 5. Mecking, H.; Kocks, U.F. Kinetics of flow and strain hardening. Acta Metal 1981, 29, 1865–1875. Copyright 2004 by Marcel Dekker, Inc. All Rights Reserved. 6. Follansbee, P.S.; Kocks, U.F. A constitutive description of the deformation of copper based on the use of the mechanical threshold stress as an internal state variable. Acta Metal 1988, 36 (1), 81–93. 7. 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[...]... their modifications (HSS and HSS-based materials and cemented tungsten carbides) These materials are used (more or less successfully) is a broad range of applications, not only for the machining of steels, but also for many other materials A major trend in the metallurgical design of these cutting tool materials is the application of standard (or slightly modified) universal tool materials using different... machining conditions by reaction of the tool material with oxygen The second section develops these ideas of self-organization for some common tool materials, and shows how they can be understood and exploited for alloys such as high-speed tool steels (HSS), cemented carbides, and cermets A deep level of understanding of the complex interactions that lead to the formation of stable secondary structures... The materials for cutting tools have traditionally been chosen for their excellent hardness and wear resistance under the extreme service conditions (high stresses and temperatures) associated with a high-speed machining operation The interaction between the tool and workpiece was once thought to lie wholly in the domain of the mechanical or physical response of the system to these conditions, and. .. surface phase transformation, resulting in the formation of oxygen-containing, stable secondary structures of the Ti–O type (see Table 2), might occur The mechanism for Ti–O formation is described in some detail below for tribological materials There is a dearth of information in the literature about the self-organization of these alloys during cutting, but it is clear that the formation of protective... Presently, tool materials based on HSS made by sintering and hot extrusion of powders also contain between 10% and 50% of high-melting compounds (e.g., Sandvik Coronites, deformed composite powder materials—DCPM [23–25]) A characteristic feature of these tool materials is the reaction of refractory compounds (carbides, carbonitrides or nitrides of titanium) during cutting, leading to the formation of... stabilization of the friction and wear parameters, in particular, by the selection of appropriate materials 3 The Features of the Self-Organizing Process During Cutting To understand the features of the self-organizing phenomenon during cutting one should understand the processes occurring at the contact surface of the ‘‘cutting tool=workpiece’’ tribosystem over a range of cutting speeds [11, 12]) Studies of cutting... build-up formation takes place The machined material transfer at the tool surface is frequently observed during the metalworking of common structural steels At the same time, oxygen (from the air) penetrates into the cutting zone Chip fragments containing Fe will react with oxygen and carbon at the tool surface and form a boundary layer of both iron carbides and oxides This leads to a built-up edge The formation... cemented carbides and ceramics 1 Frictional and Wear Behavior and Self-Organization of Adaptive Cutting Tool Materials As noted above, one of the characteristic features of cermets is associated with the formation of a thin layer of a protective secondary structure possessing some lubricity at the tool surface The formation of a stable secondary structure results in an excellent surface finish and close tolerance... correlated to the relaxation properties of the material, especially at the unstable stage of wear If the tool material has a structure that is unable to effectively transform and dissipate the energy generated by friction (a concern with the majority of traditional tool materials), damaging surface relaxation processes (e.g., adhesion to the machined part or crack formation on the tool surface) dominate during... the tool life and improved manufacturing productivity III MAJOR CUTTING TOOL MATERIALS It is possible to classify cutting tool materials according to their different characteristics and domains of application Copyright 2004 by Marcel Dekker, Inc All Rights Reserved A Universal Cutting Tool Materials The principal focus of this paper is on the so-called ‘‘universal’’ cutting tool materials and their modifications . the failure criterion. For quasi-static loading (Fig. 67a), the envel- ope is described by the Hancock=M ackenzie relation and for dynamic load- ing (Fig. 67b) by Eq. (111 ). The comparison between. creep micro-cracks. Computational Materials Science, 1996, 5, 101 110 . 100. El-Magd, E. Simulation of material behavior under impact loading. Computational Materials Sci. 1993, 1, 333–342. 101 nucleation and growth of voids. Acta Met. 1981, 29, 1509–1522. 111 . Jun, S.; Zengjie, D.; Zhonghua, L.; Mingjing, T. Fracture strength of spheroidal carbide particle. Int. J. Fract. 1990, 42, 39–42. 112 .