Abstract
A set of governing equations comprising linear momentum, mass, and heat transfer is presented for thermoelastic freezing of a porous material. The theory of unsaturated freezing porous media is introduced to model deformation of concrete, a traditional building material, whose pore network is pressurized by the wet air, frozen ice, and unfrozen water. A general solution scheme is provided for the appropriate boundary conditions pertaining to the primary concrete containment in a liquefied natural gas tank, and simulated results are analyzed for fully and partially saturated non-air-entrained concrete and fully saturated air-entrained concrete. Effect of cooling rate is also demonstrated. It is found that high cooling rate results in high expansion provoked by high hydraulic pore pressure and the corresponding suppression of pore liquid freezing temperature. It is also revealed that air-entrained concrete, by allowing quick dissipation of the displaced pore water and accommodating the ensuing ice formation, shows less contraction and subsequently less crack initiating stresses than the high-porosity, non-air-entrained concrete. Similar outcomes are observed near the concrete surfaces subjected to evaporation prior to cryogenic freezing. High hydraulic pressure, induced by the delayed dissipation of excess pore water, is likely to generate at the center of surface-dried concrete walls.
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Notes
We choose melting temperature as the reference temperature and do not consider thermal strain due to cooling from ambient temperature to the melting temperature.
The gas pressure, \(p_{G} \), is generally much smaller than the liquid and crystal pressures, but is included for completeness.
Here, we have presumed that the pressure exerted by the LNG on the inner side of the tank is negligible. Depending on the depth of the LNG in the tank, this presumption may only apply nearer to the top of the tank.
We assume that equilibrium is achieved instantly everywhere in the unsaturated strips of Fig. 6.
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Acknowledgments
This work was supported by Qatar National Research Fund (QNRF—a member of The Qatar Foundation) through NPRP 4 - 410 - 2 - 156. Any opinions, findings, and conclusions or recommendations expressed in this paper are those of the authors and do not necessarily reflect the views of the QNRF; QNRF has not approved or endorsed its content. The authors are particularly indebted to Kåre Hjorteset for providing valuable information about the concrete composite cryogenic tank structural design and insulation detail. Thanks to the reviewers and editor for their valuable comments and suggestions.
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Appendix
Appendix
1.1 Thermodynamics of Partially Saturated Freezing Concrete
The theory presented here is an application of the model proposed by Coussy (2006) for isothermal drying induced crystallization, allowing for the thermal expansion induced by the temperature change. Let us consider a porous material whose pore space is occupied by three phases: a gas referred to by index \(J = G\), a liquid referred to by index \(J = L\), and a solid crystal referred to by index \(J = C\). If \(\hbox {d}V_0 \) is the initial volume of an infinitesimal representative element from the porous solid, \(\phi _0 \) and \(\phi \) are the initial and current porosity, respectively, and the reference porous volume of the element is given by \(\phi _0 \hbox {d}V_0 \) and the current porous volume is \(\phi \hbox {d}V_0 \). The porous solid and any of its phases are capable of exhibiting infinitesimal deformation gradients. Furthermore, \(\phi _J \) if the current volume occupied by the phase J, the current overall porosity, \(\phi \) can be written as
If the current number of moles of phase J per unit initial volume is \(n_J \), temperature T, the current molar entropy is \(s_J \), and the current molar chemical potential \(\mu _J \), the Gibbs–Duhem equality for each phase J can be written in the form
such that
When no dissipation occurs, the first and second laws of thermodynamics combine to provide a Clausius–Duhem equality (for equilibrium) for a poroelastic material as given by
where \(\sigma _{ij} \) is the current overall stress components, \(\varepsilon _{ij} \) is the current overall strain component, \(\Sigma \) is the entropy of the open element per unit of its initial volume, and F is the overall Helmholtz free energy. Subscripts a and v represent air and vapor, respectively.
Let \(F_{sk} \) and \(\Sigma _{sk}\) be the Helmholtz free energy and entropy per unit initial volume of the skeleton. The term skeleton includes interfaces between the solid matrix and the phases present in the pore network and excludes the bulk phases in the pores. Due to the additive characteristics of free energy, \(F_{sk}\) and \(\Sigma _{sk} \) can be written as
With the help of (48), (49) gives us the free energy balance related to the poroelastic skeleton as
Therefore, the unsaturated poroelastic state equations can be written as
Change in partial porosities \(\phi _J \) results from the change in saturation, \(S_J \) and skeletal deformation, \(\phi _J \) resulting from the action of pressure on phases, \(p_J \). Therefore, \(\phi _J \) can be given in the form
with the constraint
Therefore, the current overall porosity is
State equations (51) account for both the energy required for skeletal deformation and energy required to create new interfaces. Using (52) with (51), these two energy variables are separated as
Substituting (52) and (55) into (50) and applying the constraint (53), we find
which leads to the following equations
\(F_{sk} \) can be divided into two parts: elastic free energy, W of the porous solid excluding the interfaces, and the interface energy, U per unit of initial porous volume \(\phi _0 \hbox {d}V_0 \). Assuming that U does not significantly vary with the skeletal deformation for constant saturation \(S_{J}\), we find
Substituting (58) into state Eq. (57), we obtain
Introducing the Legendre–Fenchel transform \(W^{*}\) of W with respect to \(\phi _J \) such that
results in
Equation (61) are the generalized state equations of unsaturated thermoporoelasticity. For a linear, isotropic thermoporoelastic material
and
Here, \(a_J \) is the linear coefficient of thermal expansion of the pore volume occupied by the phase J, and \(N_{JK} \) is the generalized Biot coupling moduli, with \(N_{JK} = N_{KJ} \) owing to the Maxwell’s symmetry relations, such that,
Here a link between the macroscopic and the microscopic properties needs to be established to determine \(b_J \) separately. This link can be set based on the microporomechanics considerations presented by (Dormieux et al. 2002) and applied by (Coussy 2006). At any stage of the freezing process, the gaseous phase and the ice crystals occupy the largest pores, and the remaining smaller pores are still filled up by the liquid water, and the crystal- and gas-filled pores can presumably act roughly the same as if they were enclosed in a porous body whose pore network was only constituted of liquid filled pores. Accordingly,
where \({K}'\) is the bulk modulus of the newly defined porous body such that,
The matrix bulk and shear moduli, \(K_s \)and \(G_s \), are intrinsic properties and do not depend on the properties of the pore network. The porosity \({\phi }'_0 \) of this porous solid is given by
Similarly, since the largest pores are occupied by the gas only, and the remaining smaller pores are filled with ice crystals and liquid water, it is therefore reasonable to assume that the wet air-filled pores are embedded in a porous matrix whose porous volume includes both the liquid filled pores and the ice filled pores. Accordingly, analogous to (66)–(68),
where
and
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Rahman, S., Grasley, Z., Masad, E. et al. Simulation of Mass, Linear Momentum, and Energy Transport in Concrete with Varying Moisture Content during Cooling to Cryogenic Temperatures. Transp Porous Med 112, 139–166 (2016). https://doi.org/10.1007/s11242-016-0636-8
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DOI: https://doi.org/10.1007/s11242-016-0636-8