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Numerical simulation of mechanical fracture test

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  • Save International Journal of M aterials Engineering 2012, 2(5): 61-66 DOI: 10.5923/j.ijme.20120205.01 Numerical Simulation of Mechanical Fracture Testings Evando E. Mede iros1, Avelino Manue l da Silva Dias2, André Luis Christoforo1,* 1Department of M echanical Engineering, Federal University of São João del Rei, São João del-Rei, 36307-352, Brazil 2Department of M echanical Engineering, Federal University of Rio Grande do Norte, Natal, 59078-970, Brazil Abstract Th is paper deals with the determination of stress intensity factors in a WC-6Co sample through the Finite Elements Method (FEM). A co mpact specimen configuration, used in fracture testings, was numerically modelled with the FEM co mmercial code MARCTM. First, in studying of this specimen was considered a bidimensional strain p lane analysis. Several meshes were used in the tested models and then results were compared with the experimental data, that can be found on technical literature. Finally, a tridimensional co mpact specimen was also modelled and studied. With these results, we were able to understand better the triaxial stress behaviour in the central portion of the specimen. It’s hopeful this methodology will be applied in nonconventional fracture mechanics testings, such as a Vic kers indentation technique. Keywords Fracture, Finite Ele ment Method, Stress Intensity Factor, Mechanical Testing 1. Introduction The study of the fracture mechanics focus on the analysis of the capacity of the material in resisting to mechanical efforts with any mistakes.The presence of small fissures can reduce the structural strength of the component, resulting in some cases, the collapse of the structure to lower stresses than acceptable stresses of project. So, the main motivation for the develop ment of the fracture mechanics was aimed at parameters to establish project criteria to take in consideration the growth of trines. Nowadays, the use of methodologies that approach the problem o f the fracture in structural materials to represent the macroscopic way through numeric models is becoming very popular. This happens because, in general, the geometric co mp lexities of the init ial conditions and of contour make it impossible the analytic resolution of these problems. In this sense, the determination of factors of stress intensity through numeric methods becomes a rational way to resolve more co mp lex problems[1]. These new approaches have been developed for the analysis of structural proble ms in different materia ls. On the other hand, the correct incorporation of mechanical aspects and inherent phenomenological to the fracture in materials is a key factor for the success and effectiveness of such predictive methodologies applicable to the nu meric analysis of the mechanical integrity of a vast number of structural components and in the most different materials[1-6]. There are a lot of methodologies used to determine the stress intensity factor through the Finite Elements Method * Corresponding author: (André Luis Christoforo) Published online at Copyright © 2012 Scientific & Academic Publishing. All Rights Reserved (FEM). There is also the method that is adopted for analysis that is of ext reme importance for the correct modeling of the singularity around the tip of the trine, in way to obtain a good representation of its field of stress and strains[7]. The current work intends to evaluate the critical stress intensity factor through computer simu lations using FEM. A conventional test of the fracture mechanics was simulated using the compact specimen (CS). In this analysis, it was used the American standart requirements ASTM E-399[8], that lies on the standard procedure for this type of experimental test. The simu lations were acco mplished being used a bidimensional and tridimensional models, in order to verify and to co mpare the results obtained with the experimental values found in the specific literature. A tridimensional model was also proposed to analyse the trines that appear during the indentation Vickers test[9]. 2. Fracture Mechanics (a) (b) (c) Figure 1. (a) Mode I – aperture; (b) Mode II – sliding; (c) Mode III – tear The fracture mechanics approaches three important variables in its study, the applied stress, the fissures size (trine) and the tenacity to the fracture of the material. In that way, the study aims at the critical co mbination of those three variables[10]. According to Figure 1, there are three basic ways of the enlargement and growth of trines, presented in the fracture mechanics. 62 Evando E. M edeiros et al.: Numerical Simulation of M echanical Fracture Testings The stress intensity factor (KI, II, III) defines the amplitude of the singularity stresses in the t ip of the trine and it is related with the geometry structure features and with the applied stresses. KI, II, III is a value that is related with the geometric features of the structure, a way of loading and also of applied stress on the same, being defined by the Lineal Elastic Fracture Mechanics(LEFM) through the Equation 1. In this calculus, σis the normal stress, a is the size of the trine and Y is a factor that depends on the way of loading and of the geometry of the structure. K I ,II ,III = Yσ π a (1) The critical stresses intensity factor in the first way of trine opening (KIC) is a mechanical property of the material (Figure 1). This value indicates a limit condit ion of propagation of fissures in mode I. In the analysis of problems of LEFM, that property has been adopted as a criterion of defect in structures and mechanical co mponents. The standart ASTM E-399[8] establishes experimental procedures that should be adopted in the tests to validate the obtaining of KIC. A quite diffused test of fracture is the one with co mpact specimen (Figure 2). be related with the stress intensity factor through Equation 4. The mathematical formu lation of integral J can be expressed by Equation 5. ( ) J IC = K 2 IC 1−ν 2 E (4) ∫ J =  wdy Γ − Ti ∂ui ∂x ds   (5) ∫ According to Figure 3, w = σ εd εij 0 ij ij is the s train energy density, Ti = σ ij n j are the co mponents of the tensile vector, nj are the co mponents of the unitary vectorΓ, ui are components of the strain vector and ds is the incre mental length along the pathΓ, E is the module of elasticity and ν the Poisson coefficient. Figure 2. Geometry of the compact specimen (ASTM E-399[8]) The thickness of specimens is related to the gradual transition of the state of equilibriu m of stress for the state of equilibriu m of strains[10]. To guarantee the existence of the stress state of equilibriu m, ASTM E-399[8] it is established some connections between the mechanical and geometric properties of the material in order to guarantee the state of equilibriu m of strains. If all those requirements for the validity of the test are followed, according to Equation 2, the value KQ found through the Equation 3 is related to an estimate of the tenacity to the fracture. In agreement with the Figure 2, in those equations a is the length of the trine, B is the thickness of the substance proof, W it is its length and σY is the limit o f the material linking. B,a ≥ 2,5 (K I ) σY 2 0,45 ≤ a W ≤ 0,55 0,25 ≤ B W ≤ 0,5 (2) Pmax ≤ 1,10 PQ KQ = PQ BW Y (3) Another parameter used in Fracture mechanics is the integral J. This parameter it is related with the energy absorbed by the material, that includes a component due to the plastic strain and other elastic one. For materials that adapts to LEFM, the rate of liberated energy is equal to the absorbed energy, soon J = G. In this case, the integral J can Figure 3. Numerical integration path to evaluate the J integral (Oller[2]) The formulation described by Equation 5 is not usual for analysis through finite elements due to the numeric difficult ies for the definition of the integration in only one way. According to Oller[2] and Dias[11], the integral is defined by the waysΓ1, Γ2, Γ3 e Γ4, according to Figure 3. 3. Methodology The simulat ions were accomplished in a sample of tungsten carbide with 6% of Cobalt (WC-6Co), whose properties are presented in the Table 1. This hard metal presents a fragile mechanical behaviour performance when submitted to tensile efforts, and elastoplastic behaviour under compression. Due to mechanical peculiarities, this material is difficu lt to analyse fro m the conventional mechanical tests, main ly due to its high superficial hardness, making it difficu lt the preparat ion of the proof substances[1 1]. Other way to determine the mechanical characteristics has been through tests that are not very conventional as, for instance, the Vickers test[9]. In both cases, the numeric analysis can come as a good alternative to evaluate the tenacity fracture of this material. International Journal of M aterials Engineering 2012, 2(5): 61-66 63 Table 1. Mechanical propert ies of WC-6Co[11, 12] E (GPa) ν H (GPa) σy (MPa) KIC (MPa·m1/2) JIC (Pa·m) 630 0,28 18,0 5760 10 146,29 Table 1, H is the Vickers hardness and JIC was obtained through Equation 4, that relates KIC with to the elastic component of integral J. In the first stage, the analysis took place through a model using isoperimetric plane elements with eight nodes. To reduce the computer effort, it took advantage of the symmetry of the problem and it was just represented its half result, according to illustrated mesh in picture 4a. The applied nodal loading was obtained through the Equation 3. In this stage, different mesh configurations were tested, aiming at reducing the nu mber of elements without having problems with the numeric results, being careful to represent the singularity around the tip of the trine[7]. In a second stage, fro m the bid imensional mesh that has used the lowest number of elements to interfere in the global results, different tridimensional meshes were also generated capable to represent this test with co mpact substances proof (Figure 4b). In th is stage isoperimetric solid elements were used with 20 knots. Again, the representation of the singularity in the tip of the trine was a carefu l procedure, being properly described. Different meshes were tested with, respectively, three hundred, six hundred and thousand and two hundred elements. To guarantee a better numeric control of these tridimensional models, was chosen to apply the load in the substance proof through its prescribed displacement, in other words, a nodal displacement corresponding to the loading result of the value of the Equation 3 was applied fo r the geometry of the specimen. value of the superficial hardness doesn´t depend on the applied load, this way it can be considered as proportional the reason between the force and the area of imp ression of the indenter. Therefore, it was possible to do the numeric analysis of the application of the load of the rigid indenter in the sample test through its prescribed displacement, allowing a better numeric control during the indentation cycle. Figure 5. Radial and surface cracks in WC-6Co (Dias et al.[1]) Using the concepts of the fracture mechanics, it was possible to establish a condition capable to identify the collapse of elements or the knots during the propagation of the trines in the indentation test. This condition would be determined through the critical stress intensity factor of WC-6Co . This way, the resolution of the fracture problem through FEM would consist on the resolution of successive lineal problems, however different fro m each other[1, 2]. At the end of each stage, the values of the stress intensity factor (KI) for different front points of the trine could be compared with the crit ical stress intensity factor (KIC) of the material, establishing the instant of the growth of the trine. 4. Results and Discussions (a) (b) Figure 4. (a) Bidimensional model of the specimen; (b) Tridimensional model In the last stage, was chosen to represent numerically the Vickers indentation test through tridimensional nu meric models. In 1983, Niihara[13], based on an experimental analysis of the performance of the elastic-plastic field of stress surgeries in the area o f the indentation together with the beginnings of the of the Lineal Elastic Fracture Mechanics, presented an expression to evaluate the WC-Co tenacity of the starting fro m the radial superficial trines that appear in these test, as represented in Figure 5. The Vickers test presents a very important particularity fro m the point of view of the nu meric simu lation, as the 4.1. Bidi mensional Models The numeric results of tenacity to the fracture were compared with the experimental value found in the literature. Table 2 presents the meshes with different nu mbers of elements, the respective applied loads, the geometric parameters of the specimen and the numeric results obtained for integral J. The meshes are described by the nu mber of elements of the complete model and for the number of elements used on the tip of the trine. The first and second meshes present a similar plenty configuration in the tip of the trine. The difference of these meshes is the geometric parameters, in other words, the size of the specimen modelled. In the third mesh, was chosen for less refined distortions in the model. A ruder mesh in the distant area of the trine proved not to influence the values 64 Evando E. M edeiros et al.: Numerical Simulation of M echanical Fracture Testings obtained for the field of stress and strains in the singular area, as well as in the value of tenacity to its fractures[7, 14]. In the other side, the reduction of the number of elements in the tip of the trine propitiated elements less distorted in this area. In the last meshes, the distortions were varied obtaining a mesh with the smallest number of elements, without committing the numeric results for JIC, being of 146,29 Pa·m for the WC-6Co studied. Table 2. Comparison between the numerical results of JIC integral for different meshes Mesh 01 Mesh 02 Mesh 03 Mesh 04 Mesh 05 Mesh 06 Load (k N) 1464,0 El ements Dimensions of CT model trine W (m) B, a (m) 427 12 2 1 J IC(Pa·m ) 144,18 66,26 411 12 0,254 0,127 144,74 66,26 112 8 0,254 0,127 144,83 66,26 104 8 0,254 0,127 144,69 66,26 94 8 0,254 0,127 144,42 66,26 60 6 0,254 0,127 144,12 hundred and thousand and two hundred elements. The numeric results obtained were very simila r and they present a discrepancy in the close areas to the free surfaces fro m the specimen. Th is can be exp lained by the fact that the stress in z direction (thickness) is null in the free surfaces. This constitutes a plan of stress, while in the central area the prevalence of a plan state of strains. According to Courtney[15], this performance induces different fracture mechanis ms and, consequently, different factors of stress intensity. In that way, the KI values tend to be larger in the central area than in the extremit ies of the structure in analysis. Besides, in that area it was obtained closer values of the JIC of the material, since the value for this property is obtained by the standart ASTM AND-399[8] in this type of plan state of strains. The distribution of the normal stress calculated in the tridimensional model of the test is illustrated in isometric v iew by the Figure 7. 4.2. Tri di mensional Models Fro m the studies done in the elaboration of the meshes for the bidimensional, we got to the mesh of nu mber six, which possesses a total of sixty ele ments, presenting a difference of 1,5% in the evaluation of JIC. In this case, the nodal displacement was of 1,52·10-5 m in the point of application of the tensile load. To reduce the computational work we adapted this mesh to represent the tridimensional model. We opted to apply the loading through the displacement prescribed in the line of application of the load, instead of calculating the loading in each knot along the thickness of the model through the function of interpolation of the used ele ment. Figure 7. Stress distribution of tridimensional model (Pa) Figure 6. Numerical distribution of the J integral along the thickness of the specimen Figure 8. Equivalent von-Mises stress distribution in tridimensional model - detail of the crack tip: (a) Lateral surface of the specimen; (b) Central face Figure 6 shows the numeric d istribution of the values of We cut twice to see the stress distribution in different integral J in the direction of the thickness of the specimen. plans in the model. The first plan studied was the view of the Three different meshes were used, with three hundred, six lateral surface, being the other obtained by a parallel cut to International Journal of M aterials Engineering 2012, 2(5): 61-66 65 the surface that goes by the center of the specimen. The analysed plans are respectively showed in Figure 8a and 8b. Due to the appearance of a σZZ stress component, the central reg ion of the specimen beco mes characterized by a triaxial stress state. Figure 9 illustrates the field distribution of von-Mises stresses at the front crack. Figure 9. σZZ normal stresses along the front of the crack in tridimensional model 4.3. Proposal for Tri dimensional Model of the Vickers test with the Merger Cracks Figure 10 shows the proposal of a tridimensional model for the indentation test that incorporates a semicircular trine in the direct ion of the diagonal of the indenter in the plan III of the illustration. The trine was positioned in the radial direction of the d iagonal of the indenter and it is in agreement with the experimental and numeric results found in the literature for WC-6Co[9, 14]. This geometry is also shown consistent with the geometry of the Palmqvist radial trine formed during the indentation test (Figure 5). The use of different meshes allowed a reduction in the number of used elements keeping the accuracy in the numeric results for JIC. Th is reduction of elements brings in a computing return, mainly in analyses with trid imensional models. The distant area fro m the trine doesn't have large influences about the stress intensity factor, soon the use of a ruder mesh in this area was also of great impo rtance to reduce the number of element used. Finally, the use of many elements in the tip area of the trine can create distorted elements, and harm the obtained results. It should be re minded that the formulation of integral J ma kes it possible an evaluation of the parameter wanted with reasonable accuracy, even in ruder meshes. In the tridimensional tests it was verified that the gradual transition of the stress plan state (in the extremities) for a triaxial state of stresses was accompanied with the appearance of a gradient of σZZ in front of the trine. The increase of that component as when it goes forward in direction to the center of the specimen provokes the increase of the equivalent von-Mises stresses. The triaxiality of the central part reduces the size of the area of plastic-strain, avoiding an increase of numeric KI of the structure. In a continuation of this work, it intends to implement a methodology to simulate the growth of a rad ial trine in the indentation test through the increment of its size in the points or nodes, being initiated when the value of the stress intensity factor reaches the critic (KI>KIC), being disconnected the nodes of the adjacent elements, increasing the trine and beginning a new analysis. The resolution of successive analyses could indicate the final form of the trine during the indentation cycle. REFERENCES [1] A. M . S. Dias, P. F. B. Sotani, G. C. Godoy. “Simulação do Ensaio de Indentação em Filmes Finos com o Uso de M odelos de Trinca Difusa”, Revista M atéria, 15, n. 3, pp. 422-430. 2010. [2] Oller, Sérgio. “FracturaM ecánica. Um Enfoque Global”, 1a Ed, Publicado por: CIM NE (Centro Internacional de M étodos Numéricos EnIngeniería), Barcelona, 286 p. 2001. [3] P. Soltani, M . Keikhosravi, R.H. Oskouei, C. Soutis, “Studying the tensile behaviour of GLARE laminates: a finite element modelling approach”. Applied Composite M aterials, 18 (4), pp. 271–282, 2010. [4] E. Barbieri, M . M eo, “A meshless cohesive segments method for crack initiation and propagation in composites”. Applied Composite M aterials, 18 (1), pp. 45–53, 2011. [5] Karthik, V., Laha, K., Parameswaran, P., Kasiviswanathan, Figure 10. Model of indentation test incorporating a radial semicircular surface crack K., Raj, B., “Small Specimen Test Techniques for Estimating the Tensile Property Degradation of M od 9Cr-1M o Steel on Thermal Aging,” J. Test. Eval.,Vol. 35, No. 4, pp. 438 – 448, 2007 5. Conclusions [6] Partheepan, G., Sehgal, D. K., and Pandey, R. K., “Finite Element Application to Estimate In-Service M aterial 66 Evando E. M edeiros et al.: Numerical Simulation of M echanical Fracture Testings Properties Using M iniature Specimen,” Int. J. M echan., Indust. Aerosp.Eng., Vol. 2, No. 2, pp. 130–136.0002-7820, 2008. [7] E. E. M edeiros, A. M . S., Dias. “Análise de Ensaios de Fratura Através do M étodo dos Elementos Finitos”, Anais do VII Simpósio de M ecânica Computacional. Araxá(M G) – Brasil. 2006. [8] ASTM (American Society for Testingand M aterials), “E399 Standard Test M ethod for Plane-Strain Fracture Toughness of M etallic M aterials”, pp. 512-532, 1990. [9] A. M . S. Dias. M odenesi, P.J., Cristina, G.C., “Computer Simulation of Stress Distribution During Vickers Hardness Testing of WC-6Co”, M aterials Research, v. 9, n. 1, pp. 73-76, 2006. [10] Anderson, T. L. “Fracture mechanics - Fundamentals and Applications”, 2nd Ed, CRC Press Inc., Boca Raton, Florida, USA, 688p. 1995. [11] A. M . S. Dias. “Análise Numérica do Processo de Fratura no Ensaio de Indentação Vickers em uma Liga de Carboneto de Tungstênio com Cobalto”, Tese de Doutorado. Universidade Federal de M inas Gerais, Belo Horizonte, Brasil, 200p. 2004. [12] E. M . Trent. “M etal Cutting”, 2nd Ed., Butterworths& Co. Press, London, England, 245p. 1984. [13] K. Niihara.“AFracture mechanics Analysis of Indentation Induced Palmqvist Crack in Ceramics”, J. M aterials Science Letters, 2, pp.221-223. 1983. [14] N. C. Santos, J., Carvalho. “Computational M ethods for the Determination of Stress Intensity Factors”, In: Proceedings of XVI International Congress on M echanical Engineering, Uberlândia – M G, Brasil.[CD-ROM ]. 2001. [15] T. H. Courtney, “M echanical Behavior of M aterials”, 1st Ed, M cGraw Hill, New York, pp. 441. 1990

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