E. Oñate^{1,2}, A. Franci^{1}, J. M. Carbonell^{1,2}
^{1} Centre Internacional de Metodes Numerics a l'Enginyeria  CIMNE, Barcelona, Spain
^{2} Universitat Politècnica de Catalunya (UPC), Barcelona, Spain
There is a large number of forming manufacturing processes in industry that involve the interaction of highly deformable continua, including viscous fluids and solids that undergo large deformations. Typically these problems also include coupled thermal effects between the interacting bodies during the forming process.
A number of numerical methods has been developed over the years for the simulation of industrial forming processes. The different methods can be classified as those based on a pure fluid mechanics formulation, i.e. the socalled flow approach developed around the 1980's [6,39,40,44,45,48] and those based on a solid mechanics formulation [11,12,19,31,47].
In this work we present a generalized continuum mechanics formulation for the analysis of industrial forming processes that involve thermally coupled interactions between deformable continua (both fluids and solids).
The motion of the deformable bodies (either a solid or a fluid) is described using a Lagrangian mixed formulation with the velocities, the pressure and the temperature as the unknown variables. Appropriate constitutive laws for the different constituent materials in the different parts of the analysis domain are used. The mixed Lagrangian formulation allows us to model the non linear interaction (including coupled thermal effects) between the different bodies involved in the forming process in a unified manner.
The continuum mechanics equations are solved with the Particle Finite Element Method (PFEM, www.cimne.com/pfem). The PFEM treats the mesh nodes in the analysis domain as virtual particles that model the behaviour of the underlying can freely move and even separate from the domain representing, for instance, the effect of water drops or cutting particles in drilling problems and machining. A mesh connects the nodes discretizing the continuum domain where the governing equations are solved using a stabilized FEM. Examples of application of PFEM to problems in fluid and solid mechanics including fluidstructure interaction (FSI) situations and coupled thermal flow problems can be found in [1,2,4,5,9,13,14,15,16,17,18,20,26,27,34,35,37,38,43]. Early attempts of the using the PFEM for solving metal forming problems were reported in [20,30].
In Lagrangian analysis procedures (such as PFEM) the motion of the virtual particles (i.e. the nodes) and of physical particles is tracked during the transient solution. Hence, the convective terms vanish in the momentum and heat transfer equations for the continuum part of the domain and no numerical stabilization is needed for treating those terms. Another source of numerical instability however remains in Lagrangian formulation, namely the treatment of incompressibility using equal order FEM interpolation for the velocities and the pressure. In this work a stabilized form of the discretized mass conservation equation is obtaining using the Finite Calculus (FIC) method proposed by Oñate et al. [21,22,23,24,25,28,29,30,36] that has excellent mass preservation features.
The generalized Lagrangian approach here described follows the ideas presented in [15] where a PFEM formulation for treating fluids and solids in a unified manner was proposed. These ideas have been extended by Franci, Oñate and Carbonell [10] using a stabilized PFEM formulation based on the FIC method.
The layout of the paper is the following. In the next section we present the basic equations for conservation of linear momentum, mass conservation and heat transfer for a continuum using a generalized Lagrangian framework. Next we derive the stabilized FIC form of the mass conservation equation. An incompressible continuum can be considered as the limit case of the compressible problem. Then the mixed finite element discretization using simplicial element with equal order approximation for the velocity, the pressure and the temperature is presented and the relevant matrices and vectors of the discretized problem are given. Details of the implicit solution of the Lagrangian FEM equations in time using an updated Lagrangian approach and a NewtonRaphson type iterative scheme are presented. The relevance of the bulk stiffness terms in the tangent matrix for enhancing the convergence and accuracy of the iterative solution for problems involving quasi and fully incompressible continua is discussed. The basic steps of the PFEM are described.
The efficiency and general applicability of the PFEM are verified by solving a set of thermally coupled industrial forming problems in two (2D) and three (3D) dimensions. The excellent performance of the numerical method proposed for all the problems analyzed is highlighted.
We will consider a domain containing a deformable material (either a fluid or a solid) which evolves in time due to external and internal forces and prescribed velocities and thermal conditions from an initial configuration at time (typically ) to a current configuration at time . The volume and its boundary at the initial and current configurations are denoted as () and (), respectively. The goal is to find the domain that the material occupies, as well as the velocities, strain rates and stresses (the deviatoric stresses and the pressure) and the temperature in the socalled updated configuration at time (Figure 1). In the following a left superindex denotes the configuration where the variable is computed.
The equations of conservation of linear momentum for a deformable continuum are written in the Lagrangian description as [3]

(1) 
In Eq.(1), is the analysis domain in the updated configuration at time with boundary , and are the velocity and body force components along the th Cartesian axis, is the density, is the number of space dimensions (i.e. for 3D problems) and are the Cauchy stresses in that are split in the deviatoric () and pressure () components as

(2) 
where is the Kronecker delta. The pressure is assumed to be positive for a tension state. Summation of terms with repeated indices is assumed in Eq.(1) and in the following.
Remark 1. The term in Eq.(1) is the material derivative of the velocity. This term is typically computed in a Lagrangian framework as

(3) 
with

(4) 
where is the value of the velocity at the material point that has the position at time and is the coordinates vector in a fixed Cartesian system [3,7,48].
The relationship between the deviatoric Cauchy stresses and the rates of deformation has the standard form for a Newtonian fluid,

(5) 
where is the viscosity, are the deviatoric rates of deformation and is the volumetric strain rate defined as .
The above constitutive equation can be written in matrix form as (for 2D problems)

(6) 
In Eq.(6) and are the deviatoric Cauchy stress vector and the strain rate vector, respectively.
We will assume a hipoelastic solid with a constitutive equation of the form

(7) 
where and are the Lame constants and is the Jaumann rate of the Cauchy stresses [3].
Tensor is approximated in this work as

(8) 
where is the determinant of the deformation tensor , and is the Lie derivative of the Kirchhoff stress tensor [3].
Combining Eqs.(7) and (8) gives the following approximation for

(9) 
Remark 2. Assumption (8) is equivalent to accepting that the Truesdell and Jaumann rates of the Cauchy stresses are identical. A more accurate assumption for solving the same problem can be found in [10].
Using standard transformations of continuum mechanics gives [3]

(10) 
where are the 2nd PiolaKirchhoff stress tensor, the upper dot denotes the time derivative and is the increment of the Cauchy stress tensor.
Substituting Eq.(10) into (9) gives after grouping terms

(11) 
where

(12) 
with

(13) 
where

(14) 
is the bulk modulus of the solid material.
The Cauchy stresses in Eq.(12) are computed on the updated configuration. These stresses can be obtained from the 2nd PiolaKirchhoff stresses on the current configuration as

(15) 
Remark 3. The relationship between the deviatoric Cauchy stress increments and the rates of deformation for a solid material can be written in the same matrix form as Eq.(6) substituting in matrix the viscosity by .
The mass conservation equation can be written for both fluid and solids as [3,7,48]

(16) 
with

(17) 
For a quasiincompressible fluid material where is the speed of sound in the fluid. For a solid material, with given by Eq.(14). Eqs.(2.3) define the constitutive equation for the pressure for both solids and quasiincompressible fluids as . This is consisted with the expression obtained in Eq.(13) for a hypoelastic solid material.
For a fully incompressible material and Eq.(16) simplifies to the standard form, . In this case the pressure increment can not be obtained from Eqs.(2.3) and then the pressure becomes an independent variable [7,48]. In our work we will retain the quasiincompressible form of for convenience.
Remark 4. Note that for Newtonian fluids the deviatoric stresses are directly related to the rates of deformation by Eq.(5), whereas for solids the deviatoric stress increments are related to the rates of deformation by Eq.(13). On the other hand, the relationship between the pressure increment and the volumetric strain rate has the form of Eq.(13) for both fluids and solids, with the adequate definition of the bulk modulus for each case.
The thermal balance equation is written in a Lagrangian framework as

(18) 
where is the temperature, is the thermal capacity, is the heat conductivity and is the external heat source.
The boundary conditions at the Dirichlet () and Neumann () boundaries with are

(19) 

(20) 
where and are the prescribed velocities and prescribed tractions on the respective boundaries and are the components of the unit normal vector to the boundary [3,7,48].

where and are the prescribed temperature and the prescribed normal heat flux at the boundaries and , respectively and is the direction normal to be boundary.
In this work we will use the following stabilized form of the mass conservation equation obtained using the Finite Calculus (FIC) approach [38]

(23) 
The last term in Eq.(23) is the socalled stabilization term introduced by the FIC technique; in this equation is a static momentum term defined as

(24) 
and is a stabilization parameter. Eq.(23) is a simplification of a more general FICbased stabilized expression for quasiincompressible fluids detailed in [38].
The stabilization parameter is typically computed for each element as

(25) 
where is the time step used for the transient solution and is a characteristic element length computed as where is the element area (for 3noded triangles) or volume (for 4noded tetrahedra). For heterogeneous material the values of and are computed at the element center [38]. For a solid material, the viscosity is substituted by with defined in Eq.(7).
We note that for “compressible” type problems not requiring stabilization. In these cases Eq.(23) recovers the standard form for the conservation of mass of the infinitesimal theory (see Eqs.(2.3)).
Multiplying Eq.(1) by arbitrary test functions with dimensions of velocity and integrating over the analysis domain gives the weighted residual form of the momentum equations as [46,48]

(26) 
Integrating by parts the term involving and using the Neumann boundary conditions (20) yields the weak variational form of the momentum equations as

(27) 
where is an arbitrary (virtual) strain rate field. Eq.(27) is the standard form of the principle of virtual power [3,7,48].
Substituting the stresses from Eq.(2) into (27) gives the following expression (in matrix form)

(28) 
In Eq.(28) and are vectors containing the test functions, the velocities and the virtual strain rates respectively; and are the body force and surface traction vectors, respectively and is an auxiliary vector. These vectors are defined as (for 2D problems)

(29) 
We multiply Eq.(23) by arbitrary (continuous) test functions (with dimensions of pressure) defined over the analysis domain. Integrating over gives

(30) 
The third integral in Eq.(30) corresponding to the stabilization term is zero in the compressible parts of the continuum.
Integrating by parts the last integral in Eq.(30) and using (24) gives after some transformations [38]

(31) 
where and are the velocity and the traction force normal to the boundary , respectively and . The characteristic length in Eq.(31) is taken as in practice.
Application of the standard weighted residual method to the thermal balance equations (18), (21) and (22) leads, after standard operations, to [46,48]

(32) 
where are the space weighting functions for the temperature.
We discretize the analysis domain into finite elements with nodes in the standard manner leading to a mesh with a total number of elements and nodes [33,46]. In our work we will choose simple 3noded linear triangles () for 2D problems and 4noded tetrahedra () for 3D problems with local linear shape functions defined for each node () of element [33,47]. The velocity components, the pressure and the temperature are interpolated over the mesh in terms of their nodal values in the same manner using the global linear shape functions spanning over the elements sharing node () [33,46]. In matrix form we have (for 2D problems)

(33) 
where

(34) 
with where is the unit matrix.
In Eq.(34) vectors , and contain the nodal velocities, the nodal pressures and the nodal temperatures for the whole mesh, respectively and the upperindex denotes the nodal value for each vector or scalar magnitude.
Substituting Eqs.(33) into Eqs.(27), (31) and (32) and choosing a Galerkin formulation with leads to the following system of algebraic equations

(35) 

(36) 

(37) 
where denotes the material time derivative of the components of a vector . The element form of the matrices and vectors in Eqs.(5) is given in Box 1.
We note that Eqs.(5) involve the geometry at the updated configuration (). This geometry is unknown; hence the solution of Eqs.(5) has to be found iteratively. The iterative solution scheme chosen in this work is presented in the next section.
Remark 5. The boundary terms of vector can be incorporated into the matrices of Eq.(36). This leads to a non symmetrical set of equations. These boundary terms are computed here iteratively within the incremental solution scheme.
Remark 6. The presence of matrix in Eq.(36) allows us to compute the pressure without the need of prescribing its value at the free surface [38].
Eqs.(5) are solved in time with an implicit NewtonRaphson type iterative scheme [3,7,47]. The basic steps within a time increment are:
In the following denotes a value computed at the th iteration.
For each iteration.
Step 1. Compute the initial Cauchy stresses for solid elements

(38) 
with

(39) 
Step 2. Compute the nodal velocity increments
From Eq.(5a)

(40) 
with the momentum residual and the iteration matrix given by

(41) 
where is the bulk tangent matrix (see Remark 9) and

(42) 
where is the tangent constitutive matrix emanating from the linearization of Eq.(35) (expressed in the current configuration) with respect to the nodal velocities [10,37]. The second term in matrix is explained in Remark 7.
Step 3. Update the nodal velocities

(43) 
Step 4. Compute the nodal pressures
From Eq.(36) we obtain

(44) 
with

(45) 
Step 5. Update the nodal coordinates and the deformation gradient

(46) 

A more accurate expression for computing can be used involving the nodal accelerations [37].
Step 6.Compute the deviatoric Cauchy stresses
Fluids:

(47) 
Solids:

(48) 
where is the tangent constitutive matrix for the deviatoric Cauchy stresses. For elastic solids and Newtonian fluids where is given by Eq.(6) and for solids.
For nonlinear continua, the adequate expression for has to be used [3,10].
Step 7.Compute the stresses
Solids:
Cauchy stresses:

(49) 
with

(50) 
2d Piola Kirchhoff stresses:

(51) 
Fluids:

(52) 
Step 8.Compute the nodal temperatures

(53) 
with

(54) 
Step 9. Check convergence
Verify the following conditions:

(55) 
where , and are prescribed error norms. In the examples presented in the paper we have set .
If conditions (55) are satisfied then make and proceed to the next time step. Otherwise, make the iteration counter and repeat Steps 1–9.
The derivatives and integrals in all the matrices of the iteration matrix are computed on the updated discretized configuration at time () while the residual vectors and are computed in the current configuration. This is a particular version of the updated Lagrangian formulation [3,10,37,47,48].
Remark 7. The tangent deviatoric constitutive matrix in Eq.(42) depends on the constitutive model chosen. For Newtonian fluids where is obtained by transforming the deviatoric constitutive tensor from the updated to the current configuration as [3,37]. Matrix is formed by applying Voigt rule to the terms of tensor . A similar expression is obtained for elastic solids changing by [10].
The second term in the integral of Eq.(42) represents the initial stress contribution to matrix [3,10,37]. Matrices and in Eq.(42) are given by (for 2D problems)


(56) 
where is the 2d PiolaKirchhoff stress tensor.
Remark 8. The iteration matrix in Eq.(40) is an approximation of the exact tangent matrix for the solid/fluid problem in the updated Lagrangian formulation [3,10,37]. The form of used in this work has yielded good results with convergence achieved for the nodal values for the velocities, the pressure and the temperature in 3–4 iterations for all the problems analyzed.
Remark 9. Including the bulk stiffness matrix in is important for the fast convergence, mass preservation and overall accuracy of the iterative solution for quasi and fully incompressible materials [9,38]. The element expression of can be obtained as [38]

(57) 
where is a positive number such that that has the role of preventing the illconditioning of the iteration matrix for highly incompressible materials. For a fully incompressible material (), a finite value of is used in practice within as this helps to obtaining an accurate solution with reduced mass loss in few iterations per time step [9]. These considerations, however, do not affect the value of within matrix in Eq.(36) that vanishes for a fully incompressible material. A similar approach for improving mass conservation in incompressible fluids was proposed in [41].
Remark 10. The time step within a time interval is chosen as where is the minimum characteristic distance of all elements in the mesh, with computed as explained in Section 3, is the maximum value of the modulus of the velocity of all nodes in the mesh and is the critical time step of all nodes approaching a solid boundary defined as where is the distance from the node to the boundary and is the velocity of the node. This definition of intends that no node crosses a solid boundary during a time step [38].
Remark 11. The material properties for the fluid and the solid may be dependent on the temperature. This effect is accounted for by updating the material properties in terms of the temperature within the iteration loop.
Let us consider a domain containing fluid and solid subdomains. Each subdomain is characterized by a set of points, hereafter termed virtual particles. The virtual particles contain all the information for defining the geometry and the material and mechanical properties of the underlying subdomain. In the PFEM both subdomains are modelled using an updated Lagrangian formulation [3,47].
The solution steps within a time step in the PFEM are as follows:
Note that the key differences between the PFEM and the classical FEM are the remeshing technique and the identification of the domain boundary at each time step.
The CPU time required for meshing grows linearly with the number of nodes. As a general rule, meshing consumes for 3D problems around 15% of the total CPU time per time step, while the solution of the equations (with typically 3 iterations per time step) and the system assembly consume approximately 70% and 15% of the CPU time per time step, respectively. These figures refer to analyses in a single processor Pentium IV PC [35]. Considerable speed can be gained using parallel computing techniques.
Application of the PFEM in fluid and solid mechanics and in fluidstructure interaction problems can be found in [1,2,4,5,8,9,13,14,15,16,17,18,20,26,27,34,35,37,38,41,43] as well in www.cimne.com/pfem.
Known velocities at boundaries in the PFEM are prescribed in strong form to the boundary nodes. These nodes might belong to fixed external boundaries or to moving boundaries linked to the interacting solids. Surface tractions are applied to the Neumann part of the boundary, as it is usual in the FEM.
Contact between fluid particles and fixed boundaries is accounted for by the incompressibility condition which naturally prevents fluid nodes to penetrate into the solid boundaries [14,26,32,35].
The contact between two solid interfaces is treated by introducing a layer of contact elements between the two interacting solid interfaces (Figure 3). This contact layer is automatically created during the mesh generation step by prescribing a minimum distance between two solid boundaries. If the distance exceeds the minimum value then the generated elements are treated as fluid elements. Otherwise the elements are treated as contact elements where a relationship between the tangential and normal forces and the corresponding displacement is introduced in [26,32,35].
This algorithm allows us to model complex frictional contact conditions between two or more interacting bodies moving in water in a simple manner. The algorithm has been used to model frictional contact situations between rigid or elastic solids in structural mechanics applications, such as soil/rock excavation problems [4,5]. The frictional contact algorithm described above has been extended by Oliver et al. [20] for analysis of metal cutting and machining problems.
Figure 3: Layer of contact elements at a soilsolid interface modelled with the PFEM 
Some examples are presented next to show the capabilities of the method for the simulation of industrial forming processes. All the problems presented involve large strains and big changes in the geometry boundaries. The “particle” description of the continuum assumed in the PFEM introduces the capability of adapting the geometry to the computed displacement solution automatically.
The numerical solution is computed taking in account thermal and mechanical effects with the solution strategy described in Section 6.
The changes in the geometry are recognized by the PFEM features. As explained in Section 7.1, the finite element mesh is obtained by a reconnection of the particles and a remeshing of the domain. A refinement of the critical areas at each time step has been performed. The criterion to detect the critical areas for refining the mesh is based on the evaluation of the plastic energy dissipation, but other mechanical variables can be used for this purpose. Details of the application of the PFEM to solid mechanics problems can be found in [4,5].
Extrusion is one of the techniques used to reduce the section of pieces of metal and form a reduced piece of the same object. This example considers a piece of steel with the dimensions shown in Figure 4 pushed towards a rigid wall die. Two different shapes of the wall die have been analysed. Both models are depicted in Figure 4. The symmetry of the problem allows us to consider only the upper part of the piece and a 2D simulation to solve the problem. The material is modelled with a thermoelastoplastic constitutive law with a HuberVon Misses yield surface. The constitutive model can be found in [42]. The physical properties of the material (steel) considered in the example are shown in Box 2.
MATERIAL PROPERTIES:  
Young Modulus  
Poisson Coefficient  0.29 
Yield Stress  
Linear Hardening Modulus ~  
Reference Hardening  
Saturation Hardening  
Hardening Exponent  16.93 
Conductivity  
Density  
Specific Capacity  
Flow Stress Softening  
Hardening Softening  
Dissipation Factor  0.9 
Expansion Coefficient 
Box 2. Material properties for the steel extrusion problem
An imposed velocity is set on the left side of the models: for the vertical die wall and for the inclined wall. In both models the vertical displacement is imposed to a zero value at the lower side of the steel plate. The initial temperature is T=293.15 K and the left boundary is fixed to this temperature during the analysis.
Figure 4: Extrusion of a steel plate with two wall dies. Dimensions expressed in mm. 
Figure 5: Extrusion of a steel plate at three time instants: t = 0.09s, t = 2.59s, t = 5.19s. Vertical die wall 
The results of the extrusion analysis with the vertical step are shown in Figures 5 and 6. Different time instants are considered, from the beginning to the end of the process. The contact forces with the wall, the temperature of the model, the plastic strain and the plastic strain rate are measures that can be obtained from the numerical results. With the distribution and the values of these quantities the extrusion process can be studied and optimized.
A similar set of results for a different extrusion problems using a die wall with a progressive reduction of the section are depicted in Figures 7 and 8.
Figure 6: Results of the extrusion of a steel plate (vertical die wall) at t = 2.59s. Nodal forces in Newtons, pressure in , temperature in Kelvins and plastic strain rate in . 
Figure 7: Extrusion of a steel plate at three time instants: t = 0.9s, t = 11.9s, t = 24.9s. Inclined die wall 
Figure 8: Results of the extrusion of a steel plate at t = 11.9s (inclined die wall). Nodal forces in Newtons, pressure in , temperature in Kelvins and plastic strain rate in . 
Figure 9: Cutting of a steel plate with a single cutter. Dimensions in mm. 
Figure 10: Cutting of a steel plate with a two symmetric cutters. Dimensions in mm. 
The next example shows the cutting of solid plate in 2D. It is a thermomechanical problem which involves large deformations and the process of cutting by means of a rigid tool. The initial conditions of the problem are depicted in Figures 9 and 10. A thermoelastoplastic constitutive law with the same material properties as described in the previous example has been used. As previously mentioned, the PFEM combines the Lagrangian updating of the configuration with a redefinition of the domain geometry. These features allow to model naturally the cutting region by refining the solid model in the tool tip and by inserting new particles (nodes) when large flat boundaries appear at the tip contact zone.
The cutting tool moves downwards with a velocity of in the single cutter model and with a velocity of in the problem with two cutters. In both models the horizontal displacement is imposed to zero in the outer sides of the plate. The initial temperature in the domain is set to 293.15 K and is kept fixed to this value in the outer boundary sides during the analysis.
The PFEM results of the material deformation and the temperature distribution for various time instants are shown in Figures 11 and 12.
Figure 11: Cutting process. Results at the onset, the middle and the end of the process using a single cutter. Nodal forces are expressed in Newtons and the temperature in Kelvins. 
Figure 12: Results at the onset, the middle and the end of a plate cutting process with two symmetric cutters. Nodal forces are expressed in Newtons and the temperature in Kelvins. 
Figure 13: Forging of a steel cylinder against to curved rigid walls. Dimensions in meters. 
The next example considers the forging of a steel cylinder. The material properties are the same as in Box 2. The mould is defined by two rigid walls that move towards each other at the same speed, () and enclose the steel piece. The dimensions of the model are depicted in Figure 13. An axisymmetric solution is considered. The initial temperature of the steel material is T =293.15 K.
The results of the material deformation, the pressure contours and the temperature distribution for various time instants are shown in Figures 14 and 15.
Figure 14: Meshes and wall nodal forces at the beginning, the middle and the end of the forging process. Nodal forces are expressed in Newtons. 
Figure 15: Pressure and temperatures at the beginning, the middle and the end of the forging process. Pressure is expressed in Pascals and the temperature in Kelvins. 
Metal hot forging consists on deforming a work piece at high temperature under compressive forces in order to obtain the desired shape of the final product. It is a largely used process in industrial metal manufacturing as it allows an improvement of the material properties of the final part via a controlled deformation process. For example, via hot forging it is possible to reduce the impurities and defects in the material, thereby avoiding stress concentrations in the final product.
The metal forging can be performed using an open die or a closed die. In this work, the latter case is considered. The geometry and the problem data for the 2D simulation are shown in Figure 16. The forging process is performed by controlling the displacement of the upper rectangular die which is pushed downwards with a velocity v=0.01 for a duration of 5.65, while the material rigid walls are kept at the same position during the analysis. At the beginning of the process the metal piece and the lower walls have temperatures T=2000 K and T =1000 K, respectively. The forging is carried out through two steps: during the first one the piece is compressed by the descending rectangular die; then the die is stopped and from t=6.0 to t=50.0 the piece is cooled down. The cooling process is carried out by applying the temperature given by the following step function to both the upper rectangular die and the internal walls.

(58) 
It is assumed that the rectangular die has the same temperature of the metal piece during the compression phase. The normal heat flux through the surfaces in contact with the air has not been taken into account in the analysis.
The metal is modelled as an isotropic incompressible nonNewtonian fluid with a nonlinear viscosity given by the following relation [44,45]

(59) 
where is the uniaxial yield stress of the material and is the deviatoric strain rate invariant defined as:

(60) 
The uniaxial yield stress depends on the temperature as follows:

(61) 
The constitutive equation (59) is typical in the study of industrial forming processes by the plastic/viscoplastic flow approach [44,45,48].
The metal piece has been discretized using 6849 3noded triangular finite elements. The 2D coupled thermalmechanical simulation has been run for 50 with =.
The snapshots of Figure 17 refer to the initial compression phase that has a duration of 5.65. The upper rectangular die moves downwards forcing the metal piece to take the shape of the lower rigid walls.
Figure 18 shows four representative snapshots of the cooling period.
Figure 16: Hot forging of a metal piece. Initial geometry, coordinates of corner points and material properties. 
Figure 17: Hot forging of a metal piece. Compression phase. Snapshots of the deformation with temperature contours at different time instants. 
Figure 18: Hot forging of a metal piece. Cooling period. Snapshots of the temperature contours on the deformed geometry at different time steps. 
Figure 19: Falling of three solid objects in a heated tank filled with a fluid. Initial geometry, thermal conditions and material properties. 
Three solid objects with the same shape fall from the same height into a tank containing a fluid at rest. The geometry, the problem data, and the initial thermal conditions are shown in Figure 19.
The fluid in the tank has an initial temperature of T=340, while the solid bodies from left to right have initial temperatures of T=180 K, T=200 K, and T=220 K, respectively. The solid and the fluid domains have been discretized with a finite element mesh of 9394 3noded triangular elements. The simulation has been run for eight seconds with =. The heat flux in the normal direction is assumed to be zero for the boundaries in contact with the air and the walls. Figure 20 shows six representative snapshots of the numerical simulation with the temperature results plotted over the fluid domain and the objects domains.
File:Draft Content 550166553Balls664.png  File:Draft Content 550166553Balls1816.png 
File:Draft Content 550166553Balls2656.png  
File:Draft Content 550166553Balls4500.png  File:Draft Content 550166553Balls7000.png 
Falling of three solid objects in a heated tank filled with a fluid. Snapshots with temperature contours at different time steps.  
Figure 20: Falling of three solid objects in a heated tank filled with a fluid. Snapshots with temperature contours at different time steps. 
Figure 21: Falling of three solid objects in a heated tank filled with a fluid. Evolution of the temperature at the center of the three objects. 
In the graph of Figure 21 the evolution of the temperature at the central point of the three solid objects is plotted.
A cylindrical ice block at initial temperature T=270 K is dropped into a tank containing water at rest at an initial temperature T=340 K. The initial geometry, the problem data and the initial thermal conditions for the 2D simulation are shown in Figure 22.
Figure 22: Melting of an ice cylinder. Geometry, material data and initial thermal conditions. 
Ice is treated as a hypoelastic solid until some of its elements reach the fusion temperature (T=273.15 K ). These elements are transferred to the fluid domain and take the physical properties of the fluid. For this analysis the following assumptions were made: the mechanical and thermal properties of water and ice do not change with temperature and the heat normal flux along the boundaries in contact with the air or the walls have been considered to be zero.
In Figure 23 snapshots of some representative instants of the analysis are shown. The temperature contours are plotted over the water domain and the ice block.
In Figure 24 the detail of the melting of the ice block is illustrated. The finite element mesh is drawn over the solid and the fluid domains.
Figure 23: Melting of an ice cylinder. Snapshots of the melting process with temperature contours at different time steps. 
Figure 24: Melting of an ice cylinder. Zoom of the ice domain at different time instants. 
A solid sphere at T=270 K is dropped into a cilndrical tank containing still water at T=340 K. In Figure 22 the geometry and the problem data are given. The 3D simulation is run for a duration of 3 with =. A finite element mesh of 144663 4noded tetrahedral elements has been used to discretize both the fluid domain and the sphere. Figure 26 shows six representative snapshots of the analysis. The temperature contours have been plotted over the fluid domain and the sphere.
Figure 27 shows the evolution of the temperature at the center of the sphere versus time. The solid material has high conductivity and this explains its fast warming. After three seconds, it practically reaches the equilibrium temperature. We note that the normal heat flux along the boundaries in contact with the air have been considered to be zero.
File:Draft Content 550166553ball3DInput.png  
Figure 25: Warming of a solid sphere with initial temperature T=270 K falling into a cylindrical tank containing a fluid at T=340 K. Initial geometry and material properties. 
Figure 27: Warming of a solid sphere (T=270 K) falling into a cylindrical tank containing a fluid at T=340 K. Evolution of the temperature at the center of the sphere. 
We have presented a unified Lagrangian formulation for analysis of industrial forming processes involving thermally coupled interactions between deformable continua containing fluids and solids. A residualbased expression of the mass conservation equation obtained using the FIC method provides the necessary stability for quasi/fully incompressible situations. The governing equations for the generalized continuum are discretized with the FEM using simplicial elements with equal linear interpolation for the velocities, the pressure and the temperature. The merits of the formulation in terms of its general applicability have been demonstrated in the solution of a variety of thermallycoupled industrial forming processes using the Particle Finite Element Method (PFEM).
This research was partially supported by the Advanced Grant project SAFECON of the European Research Council and the HFLUIDS project of the National Research Programme of Spain.
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