Now, a nonlinear SOEs is considered. Consider for example that an external force is applied at the lower left part of the FE mesh shown in Fig.
2. If the force is large enough it leads to a nonlinear response of the material and the geometry. By assumption, the nonlinearity is dominant in the lower left part of the FE mesh. A well known implicit approach to solve the nonlinear SOEs is the Newton–Raphson method [
15]. In this section, the implicit solution of the nonlinear SOEs is substructured. First, the Newton–Raphson method is summarized, then the substructuring treatment is explained. The Newton–Raphson method updates an incremental displacement vector
d with an iterative displacement vector Δ
d, using the tangent of the nonlinear SOEs
A(
d) by solving
$$ \label{lineareq} r(d) + A(d) \Delta d = 0 $$
(6)
where the residual
r(
d) defines the difference between the internal forces and the external forces
$$ r(d) = f_{\mathrm{int}}(d) - f_{\mathrm{ext}}(d) $$
(7)
the Jacobian system matrix
A(
d) or in engineering terms the effective tangent stiffness matrix is equal to
$$ A(d) = \frac{\partial r}{\partial d} = \frac{\partial f_{\mathrm{int}}}{\partial d} - \frac{\partial f_{\mathrm{ext}}}{\partial d} = k_{\mathrm{int}} - k_{\mathrm{ext}} $$
(8)
where
k
int and
k
ext are the tangent stiffness matrix and the load stiffness matrix, respectively. The linearized model is solved for the iterative change of the nodal displacements Δ
d
$$ \Delta d = -A^{-1} r $$
(9)
the iterative change of the nodal displacements are added to the total incremental nodal displacements
$$ d_{j+1} = d_{j} + \Delta d $$
(10)
where
j is the iteration number. The new nodal displacements are checked for convergence. If convergence is not achieved, the linearized model is recalculated and solved for a new Δ
d.
The nonlinear SOEs is substructured based on a dominant nonlinearity in the lower left part of the FE mesh. The FE mesh is divided into 4 equal substructures. All the nonlinearity is located at the lower left substructure, substructure number 1. At the first iteration of each increment, the substructural residual
r
s
and the substructural effective tangent stiffness matrix
A
s
are calculated for all substructures separately:
$$ \label{sub1-residual} r^{s} = \left(\begin{array}{ccc} r_{i} \\ r_{e} \end{array} \right)^{s}= \left(\begin{array}{ccc} f_{i} \\ f_{e} \end{array} \right)^{s}_{\mathrm{int}} - \left(\begin{array}{ccc} f_{i} \\ f_{e} \end{array} \right)^{s}_{\mathrm{ext}} $$
(11)
$$ \label{A-sub1} A^{s} = \left[ \begin{array}{ccc} A_{ii} & A_{ie} \\ A_{ei} & A_{ee} \end{array} \right]^{s}= \left[ \begin{array}{ccc} k_{ii} & k_{ie} \\ k_{ei} & k_{ee} \end{array} \right]^{s}_{\mathrm{int}} - \left[ \begin{array}{ccc} k_{ii} & k_{ie} \\ k_{ei} & k_{ee} \end{array} \right]^{s}_{\mathrm{ext}} $$
(12)
The substructural linearized model becomes
$$ \left(\begin{array}{ccc} r_{i} \\ r_{e} \end{array} \right)^{s}_{j+1} = \left(\begin{array}{ccc} r_{i} \\ r_{e} \end{array} \right)^{s}_{j} + \left[ \begin{array}{ccc} A_{ii} & A_{ie} \\ A_{ei} & A_{ee} \end{array} \right]^{s}_{j}\left(\begin{array}{ccc} \Delta d_{i} \\ \Delta d_{e} \end{array} \right)^{s} $$
(13)
For substructures 2–4,
r
s
and
A
s
contain the internal force contribution only since there is no external force. The iterative displacements for the internal nodes
\(\Delta d^{s}_{i}\) are expressed as function of the iterative displacements of the nodes on the boundary of the substructure
\(\Delta d^{s}_{e}\)
$$ \Delta d^{s}_{i} = \left(A^{s}_{ii,j}\right)^{-1}\left(-r^{s}_{i,j} - A^{s}_{ie,j} \Delta d^{s}_{e}\right) $$
(14)
The residual forces on the boundary nodes of substructure
s can now be written in condensed form:
$$ \label{eq_rsc} r^{s}_{c,j+1} = r^{s}_{c,j} + A^{s}_{c,j} \Delta d^{s}_{e} $$
(15)
where
$$ \label{A-sub-c} A^{s}_{c,j} = A^{s}_{ee,j} - A^{s}_{ei,j}\left(A^{s}_{ii,j}\right)^{-1}A^{s}_{ie,j} $$
(16)
$$ \label{con-residual} r^{s}_{c,j} = r^{s}_{e,j} - A^{s}_{ei,j}\left(A^{s}_{ii,j}\right)^{-1}r^{s}_{i,j} $$
(17)
The global condensed linearized model (GCLM) of the master DOFs is assembled of two contributions. The first contribution consists of
r
s
and
A
s
of the internal and the external DOFs for substructure 1. For this plastic substructure all DOFs are master DOFs. The second contribution consists of the condensed
\(r^{s}_{c}\) and
\(A^{s}_{c}\) of the external DOFs for substructures 2–4. The iterative displacement is solved by requiring
r
j + 1 = 0 from the linearized model:
$$\begin{array}{lll} \left(\begin{array}{ccc} r_{mi} \\ r_{me} \end{array} \right)^{\mathrm{gclm}}_{j+1} &=& \left(\begin{array}{ccc} r_{mi} \\ r_{me} \end{array} \right)^{\mathrm{gclm}}_{j} + \left[ \begin{array}{ccc} A_{mi-mi} & A_{mi-me} \\ A_{me-mi} & A_{me-me} \end{array} \right]^{\mathrm{gclm}}_{j}\\ &&\times\left(\begin{array}{ccc} \Delta d_{mi} \\ \Delta d_{me} \end{array} \right)^{\mathrm{gclm}} = \left(\begin{array}{ccc} 0 \\ 0 \end{array} \right)^{\mathrm{gclm}} \end{array}$$
(18)
where the subscripts
mi and
me refer to the internal DOFs contribution of substructure 1 and the external DOFs contribution of all substructures, respectively. The size of the GCLM is significantly reduced by the condensation of the internal DOFs of substructures 2–4. The GCLM is solved for the unknown Δ
d
gclm at once. The total incremental nodal displacements for the master external and internal DOFs are updated by the addition of the corresponding iterative increment Δ
d.
$$ d_{me,j+1} = d_{me,j} + \Delta d_{me} $$
(19)
$$ d_{mi,j+1} = d_{mi,j} + \Delta d_{mi} $$
(20)
The residual of substructure 1 is recalculated using Eq.
11, while the condensed substructural residual
\(r^{s}_{c}\) for substructures 2–4 are updated linearly using Eq.
15. The residual is checked for convergence by the mechanical unbalance ratio criterion. The mechanical unbalance ratio
ψ is the ratio of the
l
2 norm of the residual to the
l
2 norm of the internal force
$$ \psi = \frac{\Arrowvert r \Arrowvert}{\Arrowvert r_{int} \Arrowvert} $$
(21)
In general, the convergence is not achieved after the first iteration and more iterations are performed. The difference in treatment of the substructures becomes more clear after the first iteration. For substructure 1,
r
s
and
A
s
are recalculated by Eqs.
11 and
12. For substructures 2–4, the same value of
\(A^{s}_{c}\), that was calculated in the first iteration by Eq.
16 is used for the following iterations. The residual
\(r^{s}_{c}\) of the first iteration is updated linearly as in Eq.
15 using
\(A^{s}_{c}\) of the first iteration. The condensed linear treatment of substructures 2–4 after the first iteration significantly reduces the computing time required for the rest of iterations. The reduction of the computing time is a result of the repeated use of
\(A^{s}_{c}\) of the first iteration and the linear update of
\(r^{s}_{c}\).
Substructures 2–4 are treated linearly within an increment, but after convergence a final nonlinear evaluation is performed, based on the calculated displacements. In this evaluation, small non-linearities in the material response and geometrical non-linearities are fully considered, to a large extend correcting small errors due to the linearization.