Venugopala Swami
Punati
and
Mahesh S.
Tirumkudulu
*
Department of Chemical Engineering, Indian Institute of Technology Bombay, Powai, Mumbai, 400076, India. E-mail: mahesh@che.iitb.ac.in
First published on 15th November 2021
We investigate the drying phenomenon in polymer coatings by developing a model that accounts for the polymer-lean phase (liquid) and the polymer-rich phase (solid), while predicting the stress in the coating. The governing equations are developed for the two phases separately. In the dilute polymer region, the effect of polymer diffusion on its concentration distribution is considered. The polymer-rich phase is modeled as a porous structure, with entangled polymer chains whose diffusive motion is arrested. We employ Biot's theory to model the porous skin and to determine the stress in the coating. The governing equations are solved by employing a finite difference scheme. The effects of polymer diffusion and the skin's permeability on the coating stress are studied. We find good agreement between the predictions of the polymer concentration profile and that obtained from measurements.
The study of drying stresses has a long history though Croll was the first to systematically investigate the drying stress in polymer coatings.8–10 Croll measured the drying stress in polymer coatings (binary mixture) by applying them on a cantilever and measuring the deflection at the cantilever's endpoint during the drying process.8 He found that the final stress is independent of the coating's initial thickness and initial polymer volume fraction. Next, he presented a simple mathematical model relating stress to the polymer volume fraction, where the latter was assumed to be constant through the thickness of the coating.9 The drying stress develops once the polymer volume fraction exceeds the polymer gelation volume fraction, which corresponds to the concentration at which the film starts to exhibit solid-like mechanical properties. Experiments with two different polymer solutions showed that the fraction of solvent remaining in the film at the end of the drying process was small (about 0.1) thereby allowing the application of linear elasticity theory for determination of stress. The drying stress value obtained from linear elasticity matched well with those obtained from experiments. Experiments were also performed to determine the critical stress required for peel-off from the substrate.10 Increasing the coating thickness increases the elastic energy, leading to delamination at lower stress.
While the simple model of Croll gives a good estimate of the final stress, the drying phenomenon is more complex. The stress in drying coatings depends on the constituent materials, their mechanical properties, the drying rate and the gelation concentration of the coating material. Prediction of drying stress requires the knowledge of the coating's mechanical properties as a function of polymer concentration, the spatial distribution of the polymer concentration in all three dimensions, and spatial and temporal variation in drying rates over the surface of the film. Mathematical models were initially developed to describe the evolution of drying stress in biological materials,11,12 ceramics and clays,13–15 which were later extended to explain the drying stress in polymer coatings. Haghighi and Segerlind developed a finite element (FE) procedure to determine drying stress in agricultural products, like seeds, for a given moisture and temperature distribution in the material.11,12 They assumed a linear viscoelastic response with material properties being functions of temperature and moisture content. Later, by employing the same FE procedure, Hasatani and coworkers13–15 studied the drying-induced stresses in clays and ceramics. They assumed clay to be a linear viscoelastic material, which was approximated using a Maxwell model. They solved the heat and mass transfer equations using the finite element procedure of Haghighi and Segerlind,11,12 to determine both temperature and moisture distribution in clay. The moisture content was found to be less near surfaces exposed to drying leading to large gradients in moisture content at the surfaces. This causes differential shrinkage in the material producing tensile stress near the surfaces exposed to drying and compressive stress near the core. As drying proceeds, the moisture content at the core decreases, and the compressive stresses slowly convert into tensile stresses. Increasing the drying rate increases the maximum tensile and compressive stresses, respectively, in the outer and core portions of the film. Finally, increasing the non-uniformity in the drying rates across different surfaces warps drying clays/ceramics.15
Tam et al.16 investigated drying stress in polymer films with elasto-viscoplastic rheology, where the polymer/solvent concentration was obtained by solving the diffusion–convection equation. They determined the shrinkage in film due to change in solvent concentration and employed the finite strain theory of Lee and Liu17 to obtain stresses in drying coatings. Their one-dimensional model predicts a non-uniform polymer concentration across the thickness of the coating with the maximum found at the drying (top) surface and the minimum near the substrate. Consequently, the maximum stress in the coating is at the top surface. The peak stress in the coating decreased by decreasing the mass transfer rate at the top surface and by increasing the diffusion in the coating. They also observed that in the two-dimensional drying problem, the edge effects were negligible at a distance of four thickness lengths from the coating edge. Later, Lei et al.18,19 developed a model to predict stress in drying coatings by assuming large elastic and viscoplastic deformations.16 Their model assumes that coatings develop stress once the polymer volume fraction exceeds the gelation volume fraction. The polymer volume fraction in the coating is obtained by solving the diffusion equation for the entire film and no distinction was made between the dilute polymer regions and the gelled regions. Their model predicts that the initial solvent concentration or the final coating thickness does not influence the final drying stress in the coating. Low evaporation rates reduce the final drying stress in the coating due to stress relaxation. Depending upon the coating's relaxation time, the model allows for the coating stress to exceed the yield stress. Christodoulou et al.20 studied the drying coatings by employing conservation laws, mass transport, and mixture theory to predict the stress. The polymer network was assumed to exhibit either a nonlinear elastic or hypoelastic response. For uniform thickness coatings, it was found that drying stress in the coatings is higher if the modulus of the film is allowed to increase with polymer concentration and when yielding is arrested. Rigid spherical particles embedded in coatings over soft substrates penetrate easily into the substrate on decreasing the modulus ratio of the overcoat to the substrate, leading to the starry night effect known in the photographic industry.
Some of the models discussed above, for example in Lei et al.,18 identified that the stress in the coating originates from the skin region where the polymer volume fraction is greater than or equal to the gelation polymer volume fraction. However, the aforementioned models ignore changes in the transport properties upon skin formation, such as the rapid decrease in polymer diffusivity, which drops by orders of magnitude in the skin region.21 In contrast, Ozawa et al.22 and Okuzono et al.23 developed a model for drying in polymer coatings where such variations were accounted for. They solved the convection–diffusion equations for the polymer concentration with the diffusion coefficients for the dilute polymer region being different from the gel domain, and obtained the spatial distribution of polymer concentration in the coatings. However, their model does not predict the stress generated during drying.
Although the focus of the present work is on modeling of the drying process, measurement of drying stress plays an important role in understanding the phenomenon. Francis et al.24 provide an overview of the stress measurement studies on polymer coatings due to both drying and film curing processes. It is observed that decreasing the solvent amount in the coating at gelation reduces shrinkage after gelation; hence the drying stress in the coating decreases. This can be achieved either by decreasing the polymer glass transition temperature or by increasing the drying temperature. The stress in the coatings may also be lowered by changing the solvent type or the humidity. Coatings with slow-drying solvents and dried at high relative humidity experience lower drying stress. In such coatings, Young's modulus of the coating increases slowly during the drying process enabling the coating to relax during drying.
A recent study of direct relevance to the present investigation is that of Tomar et al.,25 who investigated the drying of polymer coatings by measuring the stress and the solvent evaporation in silicone coatings. They found that the final stress in the coating is independent of its thickness, which is consistent with earlier investigations.8 Using micro-Raman spectroscopy, they measured the polymer concentration and showed that while thin films dry uniformly, thick films form a skin at the surface. They showed that there exists a critical thickness above which the film cracks with the critical thickness decreasing with increasing stiffness of the substrate.
Despite the detailed models, to the best of our knowledge, no study has reported quantitative comparison of the predicted concentration profile and stress evolution with measurements. The work reported here aims to reduce this gap, by modeling the drying phenomenon of a binary mixture of polymer and solvent and comparing the predicted concentration profile with measurements.25 We restrict ourselves to one-dimensional drying, where all variations are only in the thickness direction. We distinguish three stages during the drying process. During the first stage, the polymer concentration everywhere is less than the gelation polymer concentration, and hence it is in a liquid form. Also, there is no resistance from the substrate to the shrinking liquid coating. Therefore, there is no stress in the coating. We solve the diffusion equation and obtain the evolution of the polymer concentration. The first stage ends when the polymer concentration at the top surface reaches the gelation polymer concentration. In the second stage, the coating contains a skin region at the top surface, where the polymer concentration is greater or equal to the gelation concentration, with the dilute polymer solution region below it. The skin thickness increases with drying, and the liquid region decreases as the solvent evaporates from the top surface. Although the skin rests over the liquid, it is assumed to be pinned to the substrate at film edges, which are far from the central region considered here. Loss of solvent leads to volume shrinkage, which in turn leads to stress development. We model the stress development by employing Biot's formulation for a porous material. The assumption of a linear model stems from Croll's measurements, where small strain (∼0.03) was recorded at the end of the drying process. The third stage of drying begins when the entire film has a polymer volume fraction greater than the gelation volume fraction with the top surface polymer volume fraction remaining less than one. Otherwise, the drying phenomenon ends with the second stage when the skin region at the top surface reaches a volume fraction of one and shuts off the drying process. In the final stage of drying, the coating contains only the skin region.
ϕ(z, t = 0) = ϕ0. | (1) |
As the drying proceeds, the evaporation rate is constant initially but with the development of the gel region at the top, the drying rate drops and solvent loss occurs via diffusion of solvent molecules from the interior of the film. Experiments of Tomar et al.25 suggest that the changing evaporation rate for the entire drying period can be captured using an exponential function,
(2) |
(3) |
(4) |
The solvent evaporates but the particles do not leave the top surface, implying a zero flux condition for the particle phase at that location. In the new reference frame, the drying problem is transformed into a filtration problem, where the substrate moves toward the top surface with a velocity . Also, the substrate is impermeable to the solvent. Hence, near the substrate, the liquid and polymer velocities are equal to that of the substrate. The boundary conditions for the liquid region become
(5) |
(6) |
Following Ozawa et al.,22 we model the diffusion coefficient D in the dilute polymer region (ϕ < ϕg) as
D = D0(1 − ϕ)ϕm, | (7) |
(8) |
Equating the rate of change of solvent in the porous network to Darcy's equation provides the governing partial differential equation for the pore pressure (p) in the skin (see Appendix C for detailed derivation),
(9) |
(10) |
(11) |
By obtaining the pressure p in the skin, the stress and strain in the skin are given by
(12) |
(13) |
The solvent flux at the top surface is equal to the evaporation rate. At the bottom surface of the skin, the polymer volume fraction is equal to ϕg. Since the polymer forms a gel at ϕg, the stress at the bottom surface of the skin is zero. The boundary conditions for the top and bottom surface of the skin become
(14) |
and
p = 0 at z = zf−, | (15) |
respectively (see Fig. 1(c)).
(16) |
(17) |
(18) |
(19) |
By solving (9) with the above boundary conditions (18) and (19), one may obtain the pressure distribution during drying of the solid phase. Substituting this pressure distribution in (12) and (13) one may evaluate the stresses and strains in the coating, respectively.
(20) |
For the liquid phase drying, by employing the dimensionless terms (20), the governing partial differential equation (4) for the polymer volume fraction ϕ becomes
(21) |
(22) |
(23) |
On substituting the dimensionless variables (20) in (9), (14) and (15), for the skin region of the liquid–skin phase drying, we have
(24) |
(25) |
and
= 0 at = f−, | (26) |
(27) |
(28) |
(29) |
For the skin phase drying, the non-dimensional form of (9) to find pressure in the skin is
(30) |
(31) |
(32) |
The stress (12) and the strain (13) in their dimensionless form are written as
(33) |
(34) |
Finally, the dimensionless forms for the evaporation rate (2), the diffusion coefficient (7), and the permeability (11), respectively, become
(35) |
= (1 − ϕ)ϕ5, | (36) |
(37) |
We solve the dimensionless governing equations for each phase by employing an implicit finite volume approach. The procedure is described in Appendix D. Care must be taken while solving the equations as the positions of the nodes change on the moving boundaries of the substrate surface and the liquid–skin interface. It is to be noted that computations are halted either when the polymer volume fraction at the top surface reaches one or when the evaporation rate is negligible.
We set the initial parameters in the drying as ϕ0 = 0.43, h0 = 120 × 10−6 m, , and μ = 4 × 10−3 Pa s. The values correspond to those observed in previously reported experiments,25 where the silicone polymer, trimethylsiloxysilicate resin, was dispersed in decamethylcyclopentasiloxane. The solidification volume fraction may be determined using the Fox equation,21 which requires the glass transition temperature of both the polymer and solvent. In the absence of reliable data of either, the gelation volume fraction was fixed at ϕg = 0.85 following Croll.9 To vary Pe and p in our computation, we varied the diffusion coefficient D0 and the permeability constant K0, respectively. Lower the diffusivity D0, higher the Peclet number Pe. And, higher the permeability K0, higher the non-dimensional number p.
First, we choose four different combinations of Pe and p and plot the polymer volume fraction ϕ(, ), see Fig. 2. In all plots, the top represents the film surface and the bottom end represents the substrate. As expected, ϕ increases in the coating with solvent evaporation, and it is maximum at the top surface ( = 0) and minimum at the substrate ( = ). As expected, the coating height () decreases as drying proceeds. Comparing Fig. 2(a) with Fig. 2(b) (or Fig. 2(c) with Fig. 2(d)), an increase in Pe causes a decreased diffusion of the polymer towards the substrate leading to a steeper concentration gradient.
As drying proceeds, ϕ reaches ϕg at the surface leading to skin formation. The vertical dashed lines in the plots represent the gelation volume fraction ϕg. On any ϕ curve, the portion to the left of ϕg-line represents the liquid region, and the portion to the right of ϕg-line represents the skin domain. At the end of liquid phase drying, the coatings with a high Pe (due to large variation in ϕ) contain a small skin region at the top and a large liquid region beneath it. As the solvent evaporates from the coating, the height of the skin region increases and the height of the liquid region decreases simultaneously, see Fig. 2(b and d). Comparing Fig. 2(b and d), one may observe that changing the permeability of the skin (p) changes evolution of ϕ during liquid-skin phase drying. Initially, when the skin forms, i.e., at ϕ = ϕg, the solvent pore pressure in the skin is g = 0. The solvent flux in the skin, the evaporation rate, and the permeability set the pressure gradient in the porous network. For a high solvent flux or evaporation rate, the pressure gradient across the skin will be large. For high permeability of the porous network, the liquid can easily flow through the skin. Hence it requires a lower pressure gradient across the skin thickness. The pressure gradient across the skin causes to vary in the skin and changes away from g. Due to the pressure in the porous network, the skin deforms to generate stress in the coating. These deformations in the porous network also cause the polymer volume fraction ϕ to change in the skin. Higher the deformation, greater is the change in ϕ of the skin. For high permeability, the pressure gradient across the skin is small; hence we see small gradients of ϕ during the liquid-skin phase drying. Consequently, increasing p leads to small deviations of ϕ from ϕg. At low Pe, Fig. 2(a and c), a large skin region forms at the top at the beginning of the liquid-skin phase drying. Due to the small liquid region, there is hardly any change in the evolution of ϕ even when p is varied over an order of magnitude during the liquid-skin phase drying. Also, the shape of the ϕ-profiles is closer to the one observed at the end of liquid phase drying. Overall, the Pe influences the concentration profile much more than the permeability.
Once the liquid-skin phase drying is over, there is only a porous network over the substrate. At this stage, the solvent evaporation from the coating's top surface changes significantly the pore pressure in the skin, which increases the polymer volume fraction everywhere in the coating. Since the properties of the skin, i.e., permeability, have been assumed to be constant in Fig. 2, the polymer volume fraction profiles in the skin do not deviate much from the one observed at the end of liquid-skin phase drying. We stop computations when the polymer volume fraction at the top surface reaches one. Because of this, some solvent remains trapped in the coating, which is in agreement with previous experiments.9
Fig. 3 plots the final stress and the thickness-averaged stress for the previous four different combinations of Pe and p. Note that the final stress value corresponds to the time when the polymer volume fraction at the top becomes one. We observe that with increasing Pe, the maximum final stress in the coating decreases. At high Pe, the skin thickness formed at the end of liquid phase drying is small (see Fig. 2). Further, the concentration at the top surface reaches one even when much of the liquid is trapped in the film. This decreases the stress (both the final maximum stress and the average stress) in coatings dried at high Pe. These results are in qualitative agreement with the observations of Tomar et al.,25 who noted low stresses for very thick films.§ Increasing the permeability p reduces the pressure gradient across the skin during drying. Therefore, the final maximum stress is reduced in magnitude but the average stress is high due to more spatial uniformity in the polymer concentration.
Fig. 3 (a) Final drying stress in the coatings with different Pe and p. (b) Evolution of the thickness-averaged drying stress in the coatings with different Pe and p. The parameters used in the computations are the same as that of Fig. 2. We stop computations when the polymer volume fraction at the top surface reaches one. The final stress distribution corresponds to this time. |
We next allow the coating parameters to vary during the drying process and plot ϕ(, ) in Fig. 4 and the average stress and the evaporation rate in Fig. 5. First, we set and as constants and allow the permeability to vary as a function of ϕ. Based on the ϕ distribution, this leads to a maximum at the bottom surface of the skin and a minimum at the top surface. Also, the solvent flux decreases as we move away from the top surface. Thus, we see a higher pressure gradient near the top surface and a lower pressure gradient near the bottom surface of the skin. When the volume fraction at the top surface reaches unity, the polymer volume fraction at the substrate is small compared to that obtained for constant . This reduces the average stress in the coatings when compared to coatings with constant , see Fig. 5(a). When ϕ reaches one, the permeability becomes zero, and the drying stops.
Fig. 4 Evolution of the polymer volume fraction in the coatings: (a) keeping and as constants while varying , (b) keeping as a constant while varying and , and (c) varying , and . The function forms for , (ϕ) and (ϕ) are given by (35), (36) and (37), respectively. In each plot, the polymer volume fraction is plotted at different non-dimensional times and the latter are noted at the bottom of the curves. The dashed vertical lines in the plots represent the polymer gelation volume fraction ϕg. Computations are obtained taking Pe = 0.017 and p = 23558. |
Fig. 5 We plot (a) the thickness-averaged coating stress and (b) the evaporation rate in the coating, while allowing its properties to change during the drying process. In (b), the left- and right-hand side insets show the evaporation rates at small and large , respectively. The parameters used in the computations are the same as that in Fig. 4. For a constant evaporation rate, the polymer volume fraction at the top surface reaches one. |
Next, the value of is held constant while and are varied as per (35) and (37), respectively. The polymer concentration variation is plotted in Fig. 4(b). As the evaporation rate decreases over time, the solvent flux in the coating decreases. Therefore, we see a smaller variation in ϕ during the liquid phase drying. In the computations, the liquid phase drying ends after satisfying ϕ = ϕg near the substrate. Thus the entire coating enters the skin phase drying without any liquid-skin phase drying. During skin phase drying, the pressure gradient across the skin is small due to the low solvent flux in the skin. Therefore, the variation in ϕ is also small. With increasing time, the evaporation rate drops to a very small value (see the right-hand side inset in Fig. 5(b)), and we hardly notice any change in the coating's properties. Therefore, the simulations are stopped when ϕ ≈ 0.98 at the top surface. As ϕ is close to unity with a uniform distribution across the coating thickness, the average stress in the coating is high compared to the previous case.
Finally, we allow all the coating parameters to vary during the drying process and plot the ϕ variation in Fig. 4(c). Since the diffusivity is an increasing function of ϕ, the diffusivity is low at initial times. Further, the evaporation rate is high at initial times. Consequently, the polymer volume fraction at the top surface increases rapidly leading to a steep concentration gradient. Once the diffusivity increases to a significant value and the evaporation rate falls, the gradient reduces and the concentration becomes more uniform across the thickness. After the coating enters the skin phase drying, and when ϕ ≈ 0.92 at the top surface, we hardly observe any change in the coating properties (because of the very low evaporation rate at long times). From the right hand-side inset in Fig. 5(b), we see that the non-dimensional evaporation rate is of the order of 10−12, which is very small. As a result, the solvent flux in the coating is negligible, and there is no change in pressure inside the skin. Therefore, the simulations are stopped at this stage and the average stress in the coating is plotted, see Fig. 5(a). The stress behavior in these coatings is similar to the previous case, i.e., it increases over time and reaches a constant value. Compared to the previous case, the final ϕ value at the top surface is smaller, with higher variation across the film thickness. This leads to a lower stress at the end of the drying period.
h0(1 − ϕ0) = hf(1 − ϕf), | (38) |
Following the experiments of Tomar et al.,25 the initial polymer volume fraction is taken to be ϕ0 = 0.43 in our computations. We set the initial coating thickness h0 = 80 μm, which at the end of drying gives hf = 40 μm. The strains reported in Tomar et al.25 during the drying are very small. Hence we consider the gelation polymer volume fraction for these coatings as ϕg = 0.9. Note that the assumed value is close to that measured by Croll8 for polystyrene in toluene (0.83) and poly(isobutyl methacrylate) (0.84). The predicted polymer volume fraction at different z is compared with the measurements for hf = 40 μm taken at the centre of the film and far from the edges of the film, see Fig. 6. The polymer volume fraction in the coating increases at all locations as the solvent evaporates from the coating. The polymer volume fraction is maximum at the top surface of the coating. As we move away from the top surface, i.e., towards the substrate, the polymer volume fraction decreases. The model predictions match well with the measured values at different z justifying the methodology adopted here. The model captures not only the initial rapid increase but also the subsequent slower increase in concentration. The transition between the two rates also occurs at about the same time as predicted.
Fig. 6 Variation of the polymer volume fraction at three different locations in the coating. The solid lines represent the model predictions, while the dashed lines with symbols represent the measurements of Tomar et al.25 The inset shows the comparison for small t. We set ϕ0 = 0.43, ϕg = 0.9, h0 = 80 μm, D0 = 2.9 × 10−11 m2 s−1 and in our simulations. |
Since the polymer concentration is below the gelation concentration, the model does not predict any stress at these times. However, experiments do show small values of stress at these early times. This is mainly because of the spatial variation of film thickness in experiments. The polymer volume fraction near the edges approach the gelation volume fraction faster than the rest of the coating due to lower thickness in these regions. The resulting skin formed at the coating edges results in stress that bends the cantilever. Such effects can only be captured when the full three dimensional problem is solved.
Future work would focus on developing a full three-dimensional drying model that accounts for the yielding and plastic deformation of the film so as to obtain a more accurate stress evolution in polymer coatings. This would require reliable measurements of the coating properties such as diffusion coefficient D, permeability k, and Young's modulus E during drying.
h(t) = hf + (h0 − hf)e−βt | (A.1) |
(A.2) |
(A.3) |
(A.4) |
J = Jp + Jl. | (B.1) |
Jp = ϕvp | (B.2) |
Jl = (1 − ϕ)vl, | (B.3) |
Jp = ϕ(vp − vl) + ϕvl. | (B.4) |
(B.5) |
(B.6) |
(B.7) |
(B.8) |
(B.9) |
Jp + Jl = C, | (B.10) |
(B.11) |
(B.12) |
(C.1) |
(C.2) |
(C.3) |
(C.4) |
During drying, the skin is not allowed to shrink due to the constraints imposed in the transverse direction. Therefore, we may write
εx = 0 and εy = 0. | (C.5) |
σx = σy = σ. | (C.6) |
σz = 0. | (C.7) |
(C.8) |
(C.9) |
On substituting (C.6)–(C.8) in (C.4), and determining the rate of liquid change in a porous material from the resulting equation one obtains
(C.10) |
(C.11) |
(C.12) |
(C.13) |
Assuming equal densities for the liquid and the polymer phases, the change in liquid content in a unit volume should equal the change in the volume of the porous material,27
(C.14) |
First, we present the discretized forms of the particle flux and the polymer volume fraction evolution equation for the liquid region. The particle flux at the face fi of the liquid region is found from
(D.1) |
(D.2) |
(D.3) |
Later, we present the liquid flux and the pore pressure evolution equations in their discretized forms. The solvent flux in the skin region at face fi is found from
(D.4) |
(D.5) |
(D.6) |
fn+1 = 0. | (D.7) |
(D.8) |
Step 1. Set.
(a) = 0 and new = 1.
(b) f = [0, d, 2d,…,Nd].
(c) g = [d/2, 3d/2,…,(2N − 1)d/2],
(d) new = [f1, g1, f2, g2,…,gN, fN+1].
(e) ϕnew = [ϕf1,ϕg1,ϕf2,ϕg2,…,ϕgN,ϕfN+1], where ϕfi = ϕgi = ϕ0.
(f) new = [f1, g1, f2, g2,…,gN, fN+1], where fi = gi = 1.
Step 2. Set dl for the computations.
Step 3. Assign ϕold = ϕnew, old = new and old = new.
Step 4. Calculate the particle flux at the faces Jfi for fi = f2, f3,…,fN.
Step 5. From the particle fluxes obtain .
Step 6. Next obtain the size of the new element, i.e..
Step 7. Obtain the particle volume fraction at the new face coordinates, i.e., either by interpolation or by extrapolation.
Step 8. Now evaluate the diffusion coefficient new at all the grid points and face points.
Step 9. Now update the time new = old + dt and the coating height .
Step 10. Now divide the new region into 2N + 1 equispaced points new and obtain ϕnew and new at these points using linear interpolation.
Step 11. Save new, new, new, ϕnew and new to files for every N1 iterations.
Step 12. Now repeat from Step 3 until (or) .
Step 1. If the liquid phase drying ends by satisfying , then go to step 2. Otherwise go to step 3.
Step 2. In this case, the entire coating becomes the skin and we do the following:
(a) We assign the values of ϕnew from the liquid region directly to the skin.
(b) We find the permeability of the skin.
(c) We know the solvent flux in the coating during the liquid phase drying. We assign this solvent flux to the skin. This sets the solvent pore pressure (, ) in the skin.
(d) By employing , we obtain stress and strain ε in the coating.
(e) We stop the liquid-skin phase drying and proceed to skin phase drying.
Step 3. In this case, the coating consists of both the skin and the liquid regions. We separate the skin and liquid regions to solve the corresponding governing equations. Before proceeding to solve the respective governing equations for liquid and skin regions, we do the following.
(a) Take the properties of the coating , , , ϕ, and from the end of liquid phase drying.
(b) Find the location in the coating, where the polymer volume fraction ϕ becomes ϕg, and assign the value to I, i.e. ϕ( = I, ) = ϕg. Here I represents the thickness of the skin (or) the location of the liquid and skin interface from the coating's top surface.
(c) Assign and ϕ of 0 ≤ ≤ I to s and ϕs, respectively.
(d) By employing ϕs, we obtain the permeability of the skin.
(e) Also, assign the solvent flux of 0 ≤ ≤ I to the skin's solvent flux, and find the pressure in the skin.
(f) Using the pressure, we obtain the stress and the strain ε in the skin region.
(g) Obtain news by dividing the skin region into 2n + 1 equal points. We now obtain ϕnews, new, new, new and εnew using interpolation. Also, obtain the solvent flux at new faces using interpolation. Here, n is the number of grid points in the skin region.
(h) Assign , ϕ and of I ≤ ≤ to l, ϕl, and l, respectively.
(i) Obtain newl by dividing the liquid region into 2N + 1 equal points. We now find ϕnewl and new using interpolation. We also find the solvent flux at new faces using interpolation. Here, N is the number of grid points in the liquid region.
(j) Finally, assign and to new and new, respectively.
(k) Save new, new, news, new, ϕnews, new, new, εnew, newl, ϕnewl and new to files.
Step 4. Set the time increment dls for the liquid-skin phase drying.
Step 5. Also, set old = new, old = new, olds = news, old = new, ϕolds = ϕnews, old = new, old = new, εold = εnew, oldl = newl, ϕoldl = ϕnewl and old = new.
Step 6. We solve the skin governing equations. For this we follow Steps 4–9 described in the next section, see Section D.3. Only difference is in the bottom boundary condition. This gives us news, new, ϕnews, new, new and εnew for the skin region. We also obtain the skin compression Δs = news,2n+1 − olds,2n+1.
Step 7. First, we shift oldl by Δs and assign it to oldl. We then calculate the solvent and particle fluxes at the new interface. By employing this particle flux, we solve the governing equations for the liquid region. For this, we follow Steps 4–8 in Section D.1 and obtain newl, ϕnewl and new. We also obtain the change in the height of the liquid region Δl = newl,2N + 1 − oldl,2N + 1.
Step 8. In the liquid region, we find out the location , where ϕl becomes ϕg. This gives us the location of the new interface znewI. Now we add this region (new skin), i.e. the region between newl,1 and znewI, to the existing skin. The properties in the new skin newns, newns, ϕnewns, newns, newns and εnewns are set by employing a procedure similar to that followed in Steps 3(c–f).
Step 9. We divide the skin (0 ≤ ≤ znewI) into 2n + 1 equal points and obtain news,f, new,f, ϕnews,f, new,f, new,f and εnew,f using interpolation.
Step 10. We divide the remaining liquid region into 2N + 1 equispaced points and obtain new,fl, ϕnew,fl and new,f using interpolation.
Step 11. Assign news = new,fs, new = new,f, ϕnews = ϕnew,fs, new = new,f, new = new,f, εnew = εnew,f, newl = new,fl, ϕnewl = ϕnew,fl and new = new,f.
Step 12. We update the time and the height of the coating by employing new = new + dls and new = old + Δs + Δl, respectively.
Step 13. Save new, new, news, new, ϕnews, new, new, εnew, newl, ϕnewl and new to files for every N2 iterations.
Step 14. If the height of the liquid region l(= new − newI) ≤ δl, we stop the iterations and save the coating properties to the files. Otherwise, we repeat the above from Step 5. Here δl is a very small value.
Step 2. Set ds for the simulations.
Step 3. Assign old = new, old = new, news, olds = news, old = new, ϕolds = ϕnews, old = new, old = new and εold = εnew.
Step 4. Obtain new by solving the finite difference equations of pressure.
Step 5. Find the polymer volume fraction ϕnew in the skin by employing the procedure described later in Appendix E, i.e. (E.4).
Step 6. Evaluate the permeability of the skin region new = (1 − ϕnew)3/(ϕnew)2.
Step 7. Evaluate the size of the elements (or ) by conserving the total amount of polymer.
Step 8. Obtain news.
Step 9. Calculate stress new and strain εnew in the coating using new.
Step 10. Obtain new,fs by dividing the skin into 2n + 1 equal segments. We then find the properties new,f, ϕnew,f, new,f, new,f, and εnew,f by employing either interpolation or extrapolation.
Step 11. Assign news = new,fs, new = new,f, ϕnew = ϕnew,f, new = new,f, new = new,f and εnew = εnew,f.
Step 12. Update the time and height of the coating using new = old + ds and , respectively.
Step 13. Save new, new, news, new, ϕnews, new, new and εnew to files for every N3 iterations.
Step 14. If ϕ1s < 1 or (or |pnew − pold| > δp), repeat the above from step 3. Otherwise, terminate the simulations and save the final properties of the coating. Here δ and δp are small values.
(E.1) |
(E.2) |
(E.3) |
(E.4) |
(E.5) |
(E.6) |
Fig. 7 Sketch for skin element while drying. The red solid lines indicate the faces and the black dashed line indicates the grid point. The black arrows at the faces indicate the flux at those faces. |
Footnotes |
† Changing the exponent to m = 3 in our computations does not change the predictions significantly. |
‡ We obtain K0 by equating the permeability obtained from (11) and eqn (6) and (7) of Buehler and Anderson30 at ϕ ≈ 0.43. At this ϕ, the value of is close to one. The predicted trend matches their measurements over a wide range of ϕ. |
§ If the coating is assumed to be elasto-viscoplastic, the situation becomes complex as drying stress may decrease with decreasing Pe, since stress relaxes more quickly in presence of viscous dissipation.24 |
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