Products: ABAQUS/Standard ABAQUS/Explicit
The behavior of granular and polymeric materials is complex. However, under essentially monotonic loading conditions rather simple constitutive models provide useful design information. These constitutive models are essentially pressure-dependent plasticity models that have historically been popular in the geotechnical engineering field. However, more recently they have also been found to be useful for the modeling of some polymeric and composite materials that exhibit significantly different yield behavior in tension and compression.
The models described here are extensions of the original Drucker-Prager model (Drucker and Prager, 1952). In the context of geotechnical materials the extensions of interest include the use of curved yield surfaces in the meridional plane, the use of noncircular yield surfaces in the deviatoric stress plane, and the use of nonassociated flow laws. In the context of polymeric and composite materials, the extensions of interest are mainly the use of nonassociated flow laws and the inclusion of rate-dependent effects. In both contexts the models have been extended to include creep.
Three yield criteria are provided in this set of models. They offer differently shaped yield surfaces in the meridional plane (p–q plane): a linear form, a hyperbolic form, and a general exponent form (see Figure 4.4.21).
The stress invariants used in the formulation are defined in Conventions, Section 1.2.2 of the ABAQUS Analysis User's Manual. The choice of model depends largely on the material, the experimental data available for calibration of the model parameters, and on the range of pressure stress values likely to be encountered.The linear model (available in ABAQUS/Standard and ABAQUS/Explicit) provides a noncircular section in the deviatoric () plane, associated inelastic flow in the deviatoric plane, and separate dilation and friction angles. The smoothed surface used in the deviatoric plane differs from a true Mohr-Coulomb surface that exhibits vertices. This has restrictive implications, especially with respect to flow localization studies for granular materials, but this may not be of major significance in many routine design applications. Input data parameters define the shape of the yield and flow surfaces in the deviatoric plane as well as the friction and dilation angles, so that a range of simple theories is provided; for example, the original Drucker-Prager model (Drucker and Prager, 1952) is available within this model.
The hyperbolic and general exponent models (available in ABAQUS/Standard only) use a von Mises (circular) section in the deviatoric stress plane with associated plastic flow. A hyperbolic flow potential is used in the meridional plane, which—in general—means nonassociated flow.
Perfect plasticity as well as isotropic hardening are offered with these models. Isotropic hardening is generally considered to be a suitable model for problems in which the plastic straining goes well beyond the incipient yield state where the Bauschinger effect is noticeable (Rice, 1975). This hardening theory is, therefore, used for processes involving large plastic strain and in which the plastic strain rate does not continuously reverse direction sharply; that is, the models are intended for problems involving essentially monotonic loading, as distinct from cyclic loading.
The isotropic hardening models can be used for rate-dependent as well as rate-independent behavior. The rate-dependent version is intended for relatively high strain rate applications.
Isotropic hardening means that the yield function is written as
The equivalent plastic strain rate, , is defined for the linear Drucker-Prager model as
The functional dependence can include hardening as well as rate-dependent effects. If the shapes of the stress-strain curves are different at different strain rates, the test data are entered as tables of yield stress values versus equivalent plastic strain at different equivalent plastic strain rates: one table per strain rate. The yield stress at a given strain and strain rate is interpolated directly from these tables.
Alternatively, when it can be assumed that the shapes of the hardening curves at different strain rates are similar, the hardening and rate dependence are specified separately. In this case we assume that the rate dependence can be written in a separable form:
Creep models are most suitable for applications that exhibit time-dependent inelastic deformation at low deformation rates. Such inelastic deformation, which can coexist with rate-independent plastic deformation, is described later in this section. However, the existence of creep in an ABAQUS material definition precludes the use of rate dependence as described above.
An additive strain rate decomposition is assumed:
where is the total strain rate, is the elastic strain rate, is the inelastic (plastic) strain rate, and is the inelastic creep strain rate. The term is omitted if the stress point is inside the yield surface, and the term is omitted if creep has not been defined or is not active.The elastic behavior can be modeled as linear or with the porous elasticity model including tensile strength described in Porous elasticity, Section 4.4.1. If creep has been defined, the elastic behavior must be modeled as linear.
In this model we define a deviatoric stress measure
With this expression for the deviatoric stress measure, the yield surface is defined as
whereIn the case of hardening defined in uniaxial compression, the linear yield criterion precludes friction angles 71.5° (3). This is not seen as a limitation since it is unlikely this will be the case for real materials.
The hardening parameter measures the cohesion of the material and represents isotropic hardening, as illustrated in Figure 4.4.23.
The formulation treats as constant with respect to stress, although it is straightforward to extend the theory to provide for the functional dependence of on quantities such as p.A method for converting Mohr-Coulomb data (, the angle of Coulomb friction, and c, the cohesion) to appropriate values of and d is described in the ABAQUS Analysis User's Manual.
Potential flow in the linear model is assumed, so that
whereComparison of Equation 4.4.2–3 and Equation 4.4.2–5 shows that the flow is associated in the deviatoric plane, because the yield surface and the flow potential both have the same functional dependence on t. However, the dilation angle, , and the material friction angle, , may be different, so the model may not be associated in the p–t plane. For the material is nondilational; and if , the model is fully associated—the model is then of the type first introduced by Drucker and Prager (1952). For and the original Drucker-Prager model is recovered.
The hyperbolic and general exponent models, which are only available in ABAQUS/Standard, are written in terms of the first two stress invariants only. The hyperbolic yield criterion is a continuous combination of the maximum tensile stress condition of Rankine (tensile cut-off) and the linear Drucker-Prager condition at high confining stress. It is written as
where , is the initial hydrostatic tension strength of the material, is the initial value of , and is the friction angle measured at high confining pressure, as shown in Figure 4.4.21(b). is the hardening parameter, which is obtained from test data:The general exponent form provides the most general yield criterion available in this class of models. The yield function is written as
where and are material parameters that are independent of plastic deformation and is the hardening parameter that represents the hydrostatic tension strength of the material, as shown in Figure 4.4.21(c). is related to test data asThe material parameters a, b, and can be given directly; or, if triaxial test data at different levels of confining pressure are available, ABAQUS will determine the material parameters from the triaxial test data. A least squares fit, which minimizes the relative error in stress, is used to obtain the “best fit” values for a, b, and .
Potential flow in the hyperbolic and general exponent models is assumed, so that
where f depends on how the hardening is defined (by uniaxial compression, uniaxial tension, or pure shear data) but can be written in general asIn both models flow is associated in the deviatoric stress plane. In the general exponent model, flow is always nonassociated in the meridional p–q plane. In the hyperbolic model comparison of Equation 4.4.2–6 and Equation 4.4.2–9 shows that the flow is nonassociated in the p–q plane if the dilation angle, , and the material friction angle, , are different. The hyperbolic model provides associated flow in the p–q plane only when and .
Classical “creep” behavior of materials that exhibit plastic behavior according to the extended Drucker-Prager models can be defined.
The creep behavior in such materials is intimately tied to the plasticity behavior (through the definition of the creep flow potential and test data), so it is necessary to define the Drucker-Prager plasticity and hardening behavior as well. The elastic part of the behavior must be linear.
The rate-independent part of the plastic behavior is limited to the linear Drucker-Prager model with a von Mises (circular) section in the deviatoric stress plane (K=1). The plastic potential is the hyperbolic flow potential described in conjunction with the hyperbolic and general exponent models (Equation 4.4.2–9).
We adopt the notion of creep isosurfaces (or equivalent creep surfaces) of stress points that share the same creep “intensity,” as measured by an equivalent creep stress. When the material plastifies, the equivalent creep surface should coincide with the yield surface; therefore, we define the equivalent creep surfaces by homogeneously scaling down the yield surface. In the p–q plane that translates into parallels to the yield surface, as depicted in Figure 4.4.27.
ABAQUS requires that creep properties be defined through the same type of test data used to define work hardening properties. The equivalent creep stress, , is determined as the intersection of the equivalent creep surface with the appropriate stress path. As a result,Figure 4.4.27 shows how the equivalent creep stress is determined when the material properties are defined via a shear test: a parallel to the yield surface is drawn, such that it passes by the material point; the intersection of such a line with the test stress path () produces .
This approach has the consequence that the creep strain rate is a function of both q and p and allows realistic material properties to be determined in cases in which, due to high hydrostatic pressures, q is very high. If one looks at the yield strength of this material to be a composite of cohesion strength and friction strength, this model corresponds to cohesion-determined creep. Thus, there is a cone in p–q space inside which there is no creep.
The built-in ABAQUS creep laws or the uniaxial laws defined through user subroutine CREEP can be used. The integration of the creep strain rate is first attempted explicitly, as described in Rate-dependent metal plasticity (creep), Section 4.3.4. If the stability limit is exceeded, a geometrically nonlinear analysis is being performed, or plasticity becomes active, the integration is done by the backward Euler method, as described in Rate-dependent metal plasticity (creep), Section 4.3.4.
The creep flow rule is derived from a creep potential, , in such a way that
where is the equivalent creep strain rate, which must be work conjugate to the equivalent creep stress:The creep strain rate is assumed to follow from the same hyperbolic potential as the plastic strain rate
where is the dilation angle measured in the p–q plane at high confining pressure; is the initial yield stress; and is a parameter, referred to as the eccentricity, that defines the rate at which the function approaches the asymptote (the creep potential tends to a straight line as the eccentricity tends to zero). This creep potential, which is continuous and smooth, ensures that the creep flow direction is always uniquely defined. The function approaches the linear Drucker-Prager creep potential asymptotically at high confining pressure stress and intersects the hydrostatic pressure axis at 90°. A family of hyperbolic potentials in the meridional stress plane is shown in Figure 4.4.26. The creep potential is the von Mises circle in the deviatoric stress plane (the -plane).Equation 4.4.2–10 and Equation 4.4.2–11 produce the complete flow rule
whereAn example of “slow” loading in which the approximation is visible is included in Verification of creep integration, Section 3.2.6 of the ABAQUS Benchmarks Manual. As is clear in the example, the effect of the approximation is small in spite of the fact that the load is ramped up over the step.
Although creep flow is associated in the deviatoric stress plane, the use of a creep potential different from the equivalent creep surface implies that creep flow is nonassociated.