Issue 24

G. Cricrì, Frattura ed Integrità Strutturale, 24 (2013) 161-174; DOI: 10.3221/IGF-ESIS.24.17 162 material becomes susceptible of bifurcations, instabilities and localized deformation modes. This is because the governing equations become hyperbolic in some unknown area of the continuum and make ill-posed the boundary value problem. As a consequence, numerical solutions chronically suffer from mesh dependency [13 - 15]. A popular and well proven in literature way to avoid this problem is the use some nonlocal formulations of the damaged material model. This is done by replacing the local variables denoting stress and strain fields, as well as the damage variables and the other internal ones, with nonlocal variables, which are space-weighted averages of the local ones. The averaging volume is related to a characteristic length l c depending from the failure evolution at the micro-structural scale. The nonlocal formulations are capable to regularize ill-posed problems associated with damage, but require a very large increasing of the computational amount with respect to the local damage formulations [16 - 19]. From the computational point of view, the regularization is strictly related to the characteristic length; in fact, with l c a constraint to the material law is introduced in addition to the large scale material behavior [20]. Also the local models can be regularized, and the easiest way to do this in a FE analysis is introducing the characteristic length not at the material model level, but more roughly at the element level. In other words, the element dimension will be strictly related to the characteristic length lc. In many works the latter computational strategy is adopted [21 - 24]. They typically present many free parameters that should be calibrated and fixed in a physically consistent way in order to make the calculation procedure effective. In the present work, a complete procedure to calculate the R-curve starting from a local form of the GTN model is presented and a numerical application on a widely used aeronautical alloy, 2024A-T351, is reported, using material and test data provided by industrial research offices. Differently from the purely phenomenological approach that is usually employed to calculate all the model parameters, a procedure to consistently calculate some of these parameters on the basis of objective micro-structural data has been performed. In order to enrich the original damage model also the defect size distribution has been considered. With such methodology, the arbitrariness of the parameters tuning is strongly reduced, and a double result is attained: the number of the FE run needed to simulate the R-curve behaviour drastically decreases, and the transferability of the whole methodology to different geometries and boundary conditions is improved. Once determined all the material parameters, to calculate the R-curve an MT fracture test has been simulated by the free FE code WARP3D. T HE GTN MODEL FOR DUCTILE FRACTURE n a homogeneous ductile metal model, the total strain amount usually leaves unchanged the volume, because the plastic part of the strain is dominant with respect to the elastic one. On the other hand, in a material model containing voids which matrix phase is ductile, the volume can globally change, due to the local plastic flow arising around the voids boundary and, consequently, the void volume change. Then, the material model response to an imposed global strain will be a stress-strain curve presenting a softening curve, nevertheless the matrix material model have hardening behaviour. In such model, the voids can grow until the global load carry capability becomes negligible. The Gurson-Tvergaard (GT) model is able to explain the local strength decreasing during the fracture process of ductile metals in the intermediate phase between the nucleation and the coalescence of voids. Standing this characteristic, in the void growth model the number of voids is kept constant. Nucleation and coalescence are taken into account before the homogenization of the material model, applying some opportune corrections, originally proposed by Needleman et al., directly to the stress-strain cell response. Updated in this way the GT model, it is usually named GTN model. Gurson-Tvergaard model The homogenization technique is based on the stress-strain characterization of a Representative Volume Element (RVE), that can be roughly defined as the minimum material volume containing all the micro-structural information of a heterogeneous material, related to the specific problem under investigation (see, e.g., [25 - 27]). In the Gurson-Tvergaard void growth model, the RVE of the material is considered as a cubic volume with a single void, yet existing in the virgin material. The initial void volume fraction f 0 should be chosen as the ‘equivalent’ volume fraction corresponding to the physical distribution of voids inside the RVE (Fig.1). The resulting homogenized material model was defined by modifying the analytical solution of the single void cell (Fig. 1) performed by Gurson and limited to a rigid-plastic material model of the matrix. The corrections take into account for the hardening of the matrix material and for the presence of void cell array instead of a single void cell. They are represented by the coefficients q 1 , q 2 , q 3 in the critical surface definition, originally introduced by Tvergaard. I