For open cracks, recall that the local damage criterion is given by
$$\begin{aligned} g({\varvec{\sigma }},d)=\frac{1}{2}{\varvec{\sigma }}:{\mathbb {S}}^{n}: {\varvec{\sigma }}-{\mathcal {R}}\left( d\right) \le 0 \end{aligned}$$
(13)
By denoting
\(\kappa ={c_{t}}/{(2c_{n})}=1-\frac{\nu }{2}\) and
\(\tau =\left\| {\varvec{\tau }}\right\|\), the damage criterion is cast into the form
$$\begin{aligned} g({\varvec{\sigma }},d)=\frac{\tau ^{2}}{\kappa }+\sigma _{n}^{2}-2c_{n} {\mathcal {R}}\left( d\right) =0 \end{aligned}$$
(14)
It is seen that material failure will take place once
\({\mathcal {R}}\left( d\right)\) reaches its maximal value at a critical damage
\(d=d_{c}\). By defining the uniaxial tensile strength
\(\sigma _{t}=\sqrt{2c_{n}{\mathcal {R}} \left( d_{c}\right) }\), the following failure function is finally achieved for both the tensile mode (
\(\tau =0\)) and the tensile-shear mode
$$\begin{aligned} g({\varvec{\sigma }})=\frac{\tau ^{2}}{\kappa }+\sigma _{n}^{2}-\sigma _{t}^{2}=0 \end{aligned}$$
(15)
Under compressive stresses with the algebraic sequence of the principal stresses
\(\sigma _{1}<\sigma _{2}<\sigma _{3}\), it is known a priori that the normal
\({\varvec{n}}\) of the critical cracking plane is located inside the plane
\(\left( {\varvec{e}}_{1},{\varvec{e}}_{3}\right)\) (see Fig.
1). For this reason, the stress tensor is written in the following form
$$\begin{aligned} {\varvec{\sigma }}=\sigma _{3}{\varvec{\delta }}+\left( \sigma _{2}-\sigma _{3}\right) {\varvec{e}}_{2}\otimes {\varvec{e}}_{2}+\left( \sigma _{1}-\sigma _{3}\right) {\varvec{e}}_{1}\otimes {\varvec{e}}_{1}. \end{aligned}$$
(16)
It follows by introducing Eq. (
16) into Eq. (
8)
$$\begin{aligned} \sigma _{n}^{c}=\sigma _{3}+\left( \sigma _{1}-\sigma _{3}\right) \left( {\varvec{e}}_{1} \cdot {\varvec{n}}\right) ^{2}-\frac{c_{n}}{d}{\varvec{ \epsilon }}^{c}:\left( {\varvec{n}}\otimes {\varvec{n}}\right) \end{aligned}$$
(17)
and
$${\varvec{\tau }}^{c}=\left( \sigma _{1}-\sigma _{3}\right) \left( {\varvec{e}}_{1}\cdot {\varvec{n}}\right) \left[ {\varvec{e}}_{1}-\left( {\varvec{e}}_{1}\cdot {\varvec{n}}\right) {\varvec{n}}\right] -\frac{c_{t}}{ d}{\varvec{\epsilon }}^{c}\cdot {\varvec{n}}\cdot \left( {\varvec{\delta }}- {\varvec{n}}\otimes {\varvec{n}}\right)$$
(18)
Further, according to the shear stress vector
\({\varvec{\tau }}\), the flow direction inside the crack plane, denoted by the unit vector
\({\varvec{t}}\) , is defined as
$${\varvec{t}}=\frac{\left( \sigma _{1}-\sigma _{3}\right) \left( {\varvec{e}}_{1}\cdot {\varvec{n}}\right) \left( {\varvec{e}}_{1}-\left( {\varvec{e}}_{1}\cdot {\varvec{n}}\right) {\varvec{n}}\right) }{\left\| \left( \sigma _{1}-\sigma _{3}\right) \left( {\varvec{e}}_{1}\cdot \varvec{n }\right) \left( {\varvec{e}}_{1}-\left( {\varvec{e}}_{1}\cdot {\varvec{n}} \right) {\varvec{n}}\right) \right\| }=\text {sign}\left( \sigma _{1}-\sigma _{3}\right) \frac{{\varvec{e}}_{1}-\left( {\varvec{e}}_{1}\cdot {\varvec{n}}\right) {\varvec{n}}}{\sqrt{1-\left( {\varvec{e}}_{1}\cdot {\varvec{n}}\right) ^{2}}}$$
(19)
The norm
\(\left\| {\varvec{\tau }}^{c}\right\|\), denoted by
\(\tau ^{c},\) can then be reformulated in terms of
\(\tau\)
$$\begin{aligned} \tau ^{c}=\tau -\frac{c_{t}}{d}{\varvec{t}}\cdot {\varvec{\epsilon }}^{c}\cdot {\varvec{n}} \end{aligned}$$
(20)
By defining the flow direction tensor
$$\begin{aligned} {\varvec{D}}={\varvec{t}}\otimes ^{s}{\varvec{n}}+\alpha {\varvec{n}} \otimes {\varvec{n}}, \ {\text {or }} \ D_{ij}=\frac{1}{2}\left( n_{i}t_{j}+n_{j}t_{i}\right) +\alpha n_{i}n_{j} \end{aligned}$$
(21)
The friction criterion is finally rearranged into the form
$$\begin{aligned} f({\varvec{\sigma }},{\varvec{\epsilon }}^{c},d)=\tau +\alpha \sigma _{n}-\frac{1}{d}{\varvec{D}}:{\mathbb {C}}^{n}:{\varvec{\epsilon }}^{c}\le 0 \end{aligned}$$
(22)
The evolution of the inelastic strain is determined by adopting an associated flow rule
$$\begin{aligned} {\dot{\varvec{\epsilon }}}^{c}=\lambda ^{s}\frac{\partial f}{\partial {\varvec{\sigma }}^{c}}=\lambda ^{s}{\varvec{D}} \end{aligned}$$
(23)
According to Eq. (
19), under monotonic loading,
\({\varvec{D}}\) is independent on the stress level. When no rotation of the principal directions occurs, the cumulated inelastic strain
\({\varvec{\epsilon }}^{c}\) can be simply measured as
\({\varvec{\epsilon }}^{c}=\Lambda ^{s} {\varvec{D}}\) with the cumulation
\(\Lambda ^{s}=\int \lambda ^{s}\) operated over the loading history. It follows
$$\begin{aligned} f({\varvec{\sigma }},{\varvec{\epsilon }}^{c},d)=\tau +\alpha \sigma _{n}-\frac{\Lambda ^{s}}{d}{\varvec{D}}:{\mathbb {C}}^{n}:{\varvec{D}}\le 0 \end{aligned}$$
(24)
On the other hand, we rewrite the damage criterion (
12) by means of the tensor
\({\varvec{D}}\)
$$\begin{aligned} g=\frac{1}{2}\left( \frac{\Lambda ^{s}}{d}\right) ^{2}{\varvec{D}}:\mathbb { C}^{n}:{\varvec{D}}-{\mathcal {R}}\left( d\right) \le 0 \end{aligned}$$
(25)
When it is satisfied, i.e.
\(g=0\), we have the relation
$$\begin{aligned} \frac{\Lambda ^{s}}{d}=2\sqrt{\frac{{\mathcal {R}}\left( d\right) }{\xi }} \end{aligned}$$
(26)
with
\(\xi =2{\varvec{D}}:{\mathbb {C}}^{n}:{\varvec{D}}=2c_{n}\left( \kappa +\alpha ^{2}\right)\).
The friction criterion is finally written in the form
$$\begin{aligned} f({\varvec{\sigma }},d)=\tau +\alpha \sigma _{n}-\sqrt{{\mathcal {R}}\left( d\right) \xi }\le 0 \end{aligned}$$
(27)
It is seen from the above friction-damage coupling analyses that friction-induced material hardening/softening is actually controlled by the kinetics of the damage resistance function
\({\mathcal {R}}\left( d\right)\). In other words, material failure will take place once
\({\mathcal {R}}\left( d\right)\) reaches its maximal value at a critical damage
\(d=d_{c}\). By defining the purely shear strength
\(\sigma _{\tau }=\sqrt{{\mathcal {R}}\left( d_{c}\right) \xi }=\sigma _{t}\sqrt{\kappa +\alpha ^{2}}\), the failure function reads
$$\begin{aligned} f({\varvec{\sigma }},d_{c})=\tau +\alpha \sigma _{n}-\sigma _{\tau }=0 \end{aligned}$$
(28)