Materials and Structures

, 50:253 | Cite as

Effect of temperature on the sorption curves of earthen materials

  • Antonin FabbriEmail author
  • Fionn McGregor
  • Ines Costa
  • Paulina Faria
Open Access
Original Article


Unfired earth is a sustainable construction material with low embodied energy, but its development requires a better evaluation of its moisture–thermal buffering abilities and its mechanical behavior. Both of them are known to strongly depend on the amount of water contained in its porous network and its evolution with external conditions (temperature, humidity), which can be assessed through several sorption–desorption curves at different temperature. However, the direct measurement of these curves is particularly time consuming (up to 2 month per curve) and thus, indirect means of their determination appear of main importance for evident time saving and economical reasons. In this context, this paper focuses on the prediction of the evolution of sorption curves with temperature on earth plasters and compacted earth samples. For that purpose, two methods are proposed. The first one is an adaptation of the isosteric method, which gives the variation of relative humidity with temperature at constant water content. The second one, based on the liquid–gas interface equilibrium, gives the variation of water content with temperature at constant relative humidity. These two methods lead to quite consistent and complementary results. It underlines their capability to predict the sorption curves of the tested materials at several temperatures from the sole knowledge of one sorption curve at a given temperature. Finally, these predictions are used to scan the range of temperature variation within which the evolution of water content with temperature at constant humidity could be neglected or should be taken into account.


Vapor sorption in porous media Latent heat of sorption/desorption Hygroscopic behavior Earthen material 

1 Introduction

Earthen materials for building construction are gaining nowadays in interest due to their large ecological potential. Indeed, they allow to drastically reduce fossil energy consumption and greenhouse gas emissions associated with the manufacture compared to conventionally used materials [1, 2]. In addition, they are known to have moisture buffering and temperature controlling properties [3, 4, 5]. At building scale, it was shown that the use of hygroscopic materials leads to a significant reduction of moisture variation amplitudes, which thus induces energy savings on ventilation and heating [6].

This is due to the microstructure of the earth, which enables hydric exchanges between the environment and water molecules on the pore surfaces through condensation/evaporation and sorption/desorption phenomena. This affinity with water molecules also significantly impacts mechanical behavior of earth materials. For example, the decrease in strength with moisture, which is well known in soil mechanics, has been demonstrated for rammed earth [7, 8, 9]. Consequently, it appears that the liquid water content of a rammed earth wall is a key parameter in order to understand the behavior and the strength of this material.

At the macroscopic scale, sorption isotherm characterizes the water uptake with increasing ambient humidity at a constant temperature, while the desorption isotherms characterizes water expulsion with decreasing ambient humidity at a constant temperature. These curves are strongly non-linear. Furthermore, a hysteresis can be observed between sorption and desorption. This phenomenon is quite common and has been widely studied by many authors for a large variety of materials like soil, wood and hemp concrete [10, 11, 12, 13]. In addition, sorption–desorption curves are known to vary with temperature. The general tendency is a small decrease of the water content at constant relative humidity as temperature rise.

It follows that a proper determination of the evolution of the water content of an hygroscopic material with the external conditions (temperature, humidity) would require to perform several sorption–desorption curves at different temperature. Knowing that the measurement of a single sorption–desorption loop on earthen material lasts from two weeks to more than two months in function on the experimental protocol, this option appears to be not acceptable for most of earthen construction projects for quite evident duration and economical reasons. Thus, any procedure which would allow to accurately assess the sorption and desorption curves from indirect measurement is of main importance.

In this context, this paper aims at proposing a method to predict the evolution of sorption curves with temperature. This effect has already been studied for a quite large range of porous materials including concrete [14], bio-based [15] and even clayey [16] materials. These studies are mainly based on the chemical equilibrium between adsorbed water and water vapor, which allows to link this temperature dependence of the sorption curves to the isosteric heat. However, since no clear data exists on the evolution of isosteric heat with temperature and relative humidity (or water content), these methods do not manage to predict the evolution of sorption–desorption curves with temperature. To overcome this problem, this paper proposes two different methods. The first one is based on the analysis of the heat of phase change in order to predict the isosteric heat evolutions. The second one is based on the link between morphology of the porous network and the water content. These two methods were applied on two kind of earthen materials: compacted earth blocks and samples of earth plasters and the obtained results were compared to experimental data which were obtained at 10 and 40 °C. At end, this approach was used in order to discuss on the impact of temperature dependency of sorption curves on hygrothermal modeling.

Finally, it is important to note that a good understanding of the earthen constructions requires taking into account their large variability, which is due to the inner nature of the material (depending on the soil location and history) and on the great numbers of construction technics (compacted earth, adobe, cob, rammed earth, plaster, extruded bricks [17]…). It is not possible, however, to explore all the possibilities at the same time. In this paper the choice of compacted earth and earth plaster has been made since it allows to encompass the behavior of a quite important number of systems. It follows that the results presented in this paper cannot be directly generalized to all earthen construction techniques.

2 Materials and methods

2.1 Material

Two kind of earth samples are tested in this paper: compacted earths and earth plasters. The raw materials used to realize the compacted earth samples come from existing centenarian rammed-earth constructions located in the Rhône-Alpes region in southeastern France: either STR from Saint-Trivier de Courtes or CRA from Cras-sur-Reyssouze. This choice ensures that the earths are suitable to construct earthen buildings. The complete characterization of these two earths is given in [8]. To sum up, the plasticity index and the Methylene Blue Value of CRA are almost twice as high as those for STR, while their grading curves are similar. These two values allow us to have a first insight on the nature of the clays within the material: the clayey proportion of STR should mainly be composed of Kaolinite and Illite, while much more active clays are expected in CRA. Having said that, the X-ray diffraction analysis of these two earths shows that their clayey proportions are both mainly composed by Illite.

The first step of the compacted samples fabrication protocol consists in crushing the rammed earth pieces of wall (which were taken directly from the construction sites) into small particles sieved through a 2-mm sieve to obtain a homogenous material. An homemade double-compaction process is then used to realize cylindrical samples of diameter 3.5 and 7 cm in height with a loading charge of 4 MPa. This charge is in the range of the one applied for the realization of compacted earth blocks with a manual press. The water content of fabrication was fixed in order to reach the higher dry density. This fabrication procedure ensures a global homogeneity of the resulting samples and a good repeatability of their main characteristics (density, compressive strength, deformability, vapor resistance factor, sorption–desorption curves). The compressed samples made with the earth CRA were referenced as C1, while the compressed samples made with the earth STR were referenced as C2.

Two earth plaster formulations, denoted by P1 and P2, were studied. The plasters P1 were composed by 25 wt% of Kaolinite (clay with a low specific surface compared to other clays; yet with a high sorption capacity compared to most minerals, whose particle size distribution is \(43\% < 2\,\upmu \hbox {m}\) and \(95\% < 80\, \upmu \hbox {m}\)), 73 wt% of sand (particle size lower than 2 mm), and 2 wt% of straw particles (size between 30 and 50 mm). The plasters P2 were composed by 31 wt% of Ascal10 (commercial fine calcareous-clay material whose particle size distribution is: \(14\% < 2\,\upmu \hbox {m}\) and \(97\% < 80\, \upmu \hbox {m}\)), 67 wt% of the same sand (particle size lower than 2 mm), and 2 wt% of straw particles (size between 10 and 30 mm). Each plaster was mixed with water (30 wt% for P1 and 24 wt% for P2) before being cast in a specific formwork (\(50 \times 50\,\hbox {cm} \times 2\) cm).

All the samples (either compacted earths or earth plasters) were dried in a controlled environment in a conditioning room at 20 ±2 °C and 55 ± 5% of relative humidity. Periodical measurements were realized to follow the drying stage of the samples, and they were not tested before a stable mass was reached. A summary of samples composition is given in the Table 1.
Table 1

Compacted earth and earth plaster compositions, water content at fabrication and dry density



Composition (wt%)

\(w_m\) (wt%)

\(\rho _d\) (\(\hbox {kg}/\hbox {m}^3\))



Earth CRA (100)





Earth STR (100)





Ka(25) Sd(73) St(2)





A10(31) Sd(67) St(2)



Ka kaolinite, A10 Ascal10, Sd sand, St straw

2.2 Determination of the sorption isotherms

Several methods exist to estimate the isothermal sorption and desorption curves, but the two most widely used are the desiccator and dynamic gravimetric vapor sorption methods.

The dynamic gravimetric sorption method, commonly called the DVS (dynamic vapor sorption) method, consists in measuring uptake and loss of moisture by flowing a carrier gas at a specified relative humidity (or partial pressure) over a small sample (from several milligrams to several grams depending on the device used) suspended from the weighing mechanism of an ultrasensitive recording microbalance. Variations in the gas’s relative humidity are automatically calculated by the device when the target condition in mass stability is reached. This method was used to draw the sorption–desorption curves at 23 and 30 °C for all the formulations with the DVS Intrinsic\(^{\copyright }\) from Surface Measurement Systems. The results are reported in the Fig. 1. Only the sorption curve is drawn to ease the reading. Whatever the material, a small but visible decrease in water content with temperature was observed. It is however important to keep in mind that the difference of temperature between the curves were quite limited (only 7 °C).
Fig. 1

Sorption curves at 23 and 30 °C for the compacted earths (a) and the earth plasters (b) obtained with the DVS method

The other method used in this paper to assess the evolution of water content with relative humidity and temperature is the desiccator method, which is precisely described in the international standard ISO 12751. The sorption stage consists in successively putting a previously dried sample in several environments of increasing relative humidity and constant temperature. The sample is periodically weighed and it stays within a given environment until constant mass. The desorption stage consists in successively putting a sample previously equilibrated at 95% (at least) in several environments of decreasing relative humidity until mass is constant and at constant temperature.

The relative humidity within the desiccators is fixed by equilibrium with saturated saline solutions through the activity of its solvent (that is liquid water). This latter tends to decrease with salt concentration, but it is also impacted by the nature of the salt, the temperature, etc. The value of the equilibrium relative humidity at saturation for a dozen salts of different solubility levels and at several temperatures is given in the standard. However, this value remains quite theoretical, and it can be modified by a great number of factors like impurities in salts or water, non-saturation of the saline solution at the liquid–gas interface… To avoid this problem, the effective relative humidity in the desiccators near the samples have been measured with Rotronic HygroLog HL-NT sensors. The salts which were used in this study as well as the target and measured relative humidity within the desiccators are summarized in Table 2.

Using this protocol, a sorption–desorption loop can be made in approximatively 2 months for earthen materials, while only a period of 2 weeks is necessary if the DVS method is used. On the other hand, the desiccator method can test several specimens at the same time, and it is the only way to test materials with high levels of heterogeneity because of the small dimensions of DVS samples.
Table 2

Summary of the salts used in this study, their equilibrium relative humidity (in %) as it is given in the standard ISO 12751 (Targ), and the measured relative humidity in the desiccators (Meas)


\(\hbox {KC}_2\hbox {H}_3\hbox {O}_2\)



\(\hbox {KNO}_3\)

10 °C Targ





10 °C Meas

28.5 ± 2

61 ± 2

79 ± 2

99 ± 2

23 °C Targ





23 °C Meas

24.5 ± 2

56.5 ± 2

78 ± 2

98.5 ± 2

40 °C Targ




40 °C Meas

22 ± 2

51 ± 2

77 ± 2

98 ± 2

Whatever method used, the isothermal sorption curves should be intrinsic to the tested material. However, direct comparisons between the curves obtained by the DVS or the desiccator methods is not possible since, as it is already underlined by Labat et al. [18], the reference dry mass used to calculated the water content is intrinsically different for the two methods: the dry mass considered by the DVS is obtained by drying the sample through a flow of dry air, while the dry mass for the desiccator method is commonly estimated from the drying at 105 °C.

One option to compare the two methods should be to dry the DVS sample in an oven at 105 °C after (or before) the sorption–desorption test. If this dry mass, denoted by \(m_\mathrm{d}^{105\,^{{\circ }}\hbox {C}}\), is taken as the reference, the water content given by the DVS, denoted by \(w_\mathrm{DVS}\), must be corrected as follows:
$$\begin{aligned} w_\mathrm{DVS}^{\rm corrected}=\left( \frac{m_\mathrm{d}^{105\,^{{\circ }}\hbox {C}}}{m_\mathrm{d}^{23\,^{{\circ }}\hbox {C}}} \right) (w_\mathrm{DVS}+1)-1 \end{aligned}$$
where \(m_\mathrm{d}^{23\,^{{\circ }}\hbox {C}}\) is the dry mass obtained at 23 °C under the dry atmosphere of the DVS. However, the oven drying stage is particularly complicated to perform. Indeed, since the sample mass for the DVS is extremely low (around 1 g), any dust supply or release may significantly change the results. To avoid this complexity, another option is to modify the desiccator experimental protocol by adopting a drying process similar to the DVS’s one. For that purpose, a vacuum drying at 23 °C within a dessicator with silica gel, insuring a relative humidity lower than 5% during at least the whole drying period (approx. 2 weeks), was used in this study.
Fig. 2

Comparison between the sorption curves obtained with the DVS and with the dessicator method depending on the dry mass correction for the earth plaster P1 (a) and the compacted earth samples C1 (b)

The isothermal sorption curves of compacted earth C1 and earth plaster P1 at 23 °C for the two methods (either DVS or dessicator) and the two kinds of reference dry mass (either \(m_\mathrm{d}^{105\,^{{\circ }}\hbox {C}}\) or \(m_\mathrm{d}^{23\,^{{\circ }}\hbox {C}}\)) are showed in the Fig. 2. This comparison gives some confidence on the consistency between DVS and dessicator methods if the same protocol is used to estimate the dry mass. In the following of this study, for convenient purpose, no correction was applied on the DVS results and the dry mass of the desiccator method, which is also used to calculate the dry density, was determined using the vacuum drying procedure at 23 °C.

3 Sorption curve and enthalpy of phase change

3.1 Integral and differential enthalpy of phase change

The natural definition of the specific enthalpy of desorption is the difference between the specific enthalpies of the vapor and of the adsorbed water, denoted by \(\Delta h_\mathrm{v}\). If thermodynamical equilibrium is assumed between adsorbed water and water vapor, it is linked to the specific entropy of these two phases (denoted by \(s_{\rm L}\) for adsorbed water and by \(s_{\rm v}\) for water vapor) through the equation (proof in “Appendix”):
$$\begin{aligned} \Delta h_\mathrm{v} = T (s_\mathrm{v} - s_\mathrm{L}) \end{aligned}$$
where T is the temperature at which the phase change occurs. Using the expression of \(s_{\rm L}\) and \(s_{\rm v}\) reported in the “Appendix”, the Eq. (2) becomes:
$$\begin{aligned} \Delta h_\mathrm{v} = L_\mathrm{e} + (C_\mathrm{v}-C_\mathrm{L}) (T-T_\mathrm{e}) - \frac{R T}{M_{\text{H}_{2}\text{O}}} \ln \varphi \end{aligned}$$
where \(L_\mathrm{e}=2.26\,\hbox {MJ}/\hbox {kg}\) is the specific latent heat of evaporation of free water at boiling temperature, denoted by \(T_\mathrm{e} = 373\,\hbox {K}\), \(R = 8.31\,\hbox {J}/\hbox {mol}/\hbox {K}\) is the perfect gas constant, \(M_{\text{H}_{2}\text{O}}=18\,\hbox {g}/\hbox {mol}\) is the molar mass of water, while \(C_\mathrm{v}=1616\,\hbox {J}/\hbox {kg}/\hbox {K}\) and \(C_\mathrm{L}=4185\,\hbox {J}/\hbox {kg}/\hbox {K}\) are respectively the specific heat of vapor and adsorbed water, which are assumed to be constant. Finally, \(\varphi\) is the relative humidity, which is defined as the ratio between the partial pressure of vapor at which the phase change occurs (\(p_{\rm v}\)) and the partial pressure of vapor at saturation (\(p_{\rm v}^{\rm sat}\)).

The last term of (3), namely \((-R T/M_{\text{H}_{2}\text{O}}) \ln \varphi\) leads to an increase in \(\Delta h_\mathrm{v}\) when the equilibrium relative humidity decreases. As is depicted by the Eq. (2) this stems from the quite logical increase of vapor entropy when the concentration of vapor molecules within the air phase decreases. Note that \(\varphi\) in this expression is the relative humidity at the local sorption/desorption front (that is the interface between adsorbed water and water vapor). For free pure water, the relative humidity at the evaporation/condensation front is always equal to 1, and thus this last term vanishes. However, it is almost always neglected even for confined adsorbed in-pore water (for which \(\varphi < 1\) at the liquid–gas interface), while as already discussed by Soudani et al. [5], the variations of \(\Delta h_\mathrm{v}\) with T and \(\varphi\) appear to be on the same order of magnitude. Let us eventually notice that the expression (3) is based on the assumption that the entropy of adsorbed water only depends on temperature. This assumption will surely be wrong at very low saturation where strong interactions occur between adsorbed water and pore walls. In such case, an additional corrective term should be added, but its quantification is out of the scope of this paper.

Another way to assess the enthalpy of phase change is to use the differential specific internal energy and entropy of the adsorbed phase, respectively denoted by \(\dot{u}_\mathrm{L}\) and \(\dot{s}_\mathrm{L}\), and defined as
$$\begin{aligned} \dot{u}_\mathrm{L} = \frac{1}{\rho _\mathrm{d}} \left( \frac{\partial U_\mathrm{L}}{\partial w}\right) _{T} ; \dot{s}_\mathrm{L} = \frac{1}{\rho _\mathrm{d}} \left( \frac{\partial S_\mathrm{L}}{\partial w}\right) _{T} \end{aligned}$$
where \(w=m_{\rm L}/m_\mathrm{d}\), with \(m_{\rm L}\) the mass of adsorbed and/or liquid water and \(m_\mathrm{d}\) the dry mass, is the gravimetric water content, while \(U_\mathrm{L}\) and \(S_\mathrm{L}= \rho _\mathrm{d} w s_{\rm L}\) are the internal energy and the entropy of the adsorbed phase per unit of initial total volume of the material and \(\rho _\mathrm{d}\) is the dry density.
The combined use of these notations with the chemical equilibrium condition provides:
$$\begin{aligned} \Delta \dot{h} = h_\mathrm{v} -\dot{u}_\mathrm{L} = T (s_\mathrm{v}-\dot{s}_\mathrm{L}) \end{aligned}$$
By analogy with the Eq. (2), \(\Delta \dot{h} = h_\mathrm{v} - \dot{u}_\mathrm{L}\) is defined as the differential enthalpy of desorption. It is also commonly called isosteric heat. This form of the enthalpy of phase change is particularly interesting because it satisfies the following Clapeyron-like equation (proof in “Appendix”):
$$\begin{aligned} \Delta \dot{h} = - \frac{R}{M_{\text{H}_{2}\text{O}}} \left( \frac{\partial \ln p_\mathrm{v}}{\partial 1/T} \right) _{w} \end{aligned}$$
It follows that \(\Delta \dot{h}\) can be experimentally determined from the analysis of the sorption–desorption curve variations with temperature. If the two temperatures remain sufficiently close, it is possible to ignore the variation of \(\Delta \dot{h}\) with temperature, and the integration of the Eq. (31), which is reported in the “Appendix”, provides:
$$\begin{aligned} \Delta \dot{h} (T_{m},w) = - \frac{R}{M_{\text{H}_{2}\text{O}}} \ln \left( \frac{p_\mathrm{v}(T_2,w)}{p_\mathrm{v}(T_1,w)}\right) \frac{T_1 T_2}{T_1-T_2} \end{aligned}$$
where ω is the water content, which is held constant, \(T_1\) and \(T_2\) are the two temperatures at which the sorption–desorption curves are drawn, \(T_{m} = (T_1 + T_2)/2\) is the average temperature, while \(p_\mathrm{v}(T_1,w)\) and \(p_\mathrm{v}(T_2,w)\) are the vapor pressure at equilibrium with the water content w for the temperatures \(T_1\) and \(T_2\), respectively.
The combination of equations (2) and (5) leads to the following relation between \(\Delta h_\mathrm{v}\) and \(\Delta \dot{h}\):
$$\begin{aligned} \Delta h_\mathrm{v} - \Delta \dot{h} = T w \frac{\partial s_{\rm L}}{\partial w} \end{aligned}$$
Under the assumption that \(s_{\rm L}\) only depends on the temperature, the term \(\partial s_{\rm L}/\partial w\) becomes null and the isosteric heat (\(\Delta \dot{h}\)) can henceforth be assumed to be equal to the integral enthalpy of the phase change (\(\Delta h_\mathrm{v}\)). A way to check this assumption is to compare the values of \(\Delta h_\mathrm{v}\) given by the Eq. (2) and the differential enthalpy estimated from the isosteric method on sorption curves at 23 and 30 °C for each tested materials. The results are reported in the Fig. 3. The experimental points appear to be quite scattered, in particular at low humidity. This may be due to measurement uncertainties, since an error of 3% in the measurement of the relative humidity leads to a theoretical relative error of approximatively 20% in \(\Delta \dot{h}\) at 10%rh. This error becomes lower than 1% when the relative humidity is higher than 30%. Anyway, this graph underlines that the global tendency of calculated values of \(\Delta h_\mathrm{v}\) and the estimated ones for \(\Delta \dot{h}\) is the same, that is an increase of the enthalpy of desorption when the relative humidity decreases. Thus, even if they can not be considered as hard proofs, these results give some confidence on the validity of this approach for the materials considered in this study.
Fig. 3

Evolution of the enthalpy of phase change with relative humidity estimated from the Clapeyron equation (dots) and from the Eq. (3) (line)

3.2 Isosteric method: variation of relative humidity with temperature at constant water content

Alternatively, the combined use of the Eq. (7) and the assumption \(\Delta h_\mathrm{v} = \Delta \dot{h}\) can be used to estimate the evolution of sorption curve with temperature:
$$\begin{aligned} \frac{\varphi (w,T_2)}{\varphi (w,T_1)} = \frac{p_{\rm v}^{\rm sat}(T_1)}{p_{\rm v}^{\rm sat}(T_2)} \exp \left( \frac{-\Delta h_\mathrm{v} M_{\text{H}_{2}\text{O}}}{R} \frac{T_1-T_2}{T_1 T_2}\right) \end{aligned}$$
Throughout the rest of the paper, this way to estimate the variation of sorption curve with temperature is called the “isosteric method”.

The difference between the sorption curves at 23 and 30 °C is not sufficient in order to scan the accuracy of this method. In consequence, the comparison is made between sorption curves of the same samples at 10 and 40 °C. Due to technical limitation of the DVS which is used in this study, the sorption curves are obtained with the desiccator method with the salts reported in the Table 2. In addition, only the compacted earth C1 and the earth plaster P1 have been tested.

Calculations are made using the sorption curve at 23 °C obtained with the DVS as a reference. In other words, the Eq. 9 is used with \(T_1 = 296\,\hbox {K}\) while \(T_2 = 283\,\hbox {K}\) to build the sorption curve at 10 °C, and \(T_2=313\,\hbox {K}\) for the sorption at 40 °C. The results, are shown in Fig. 4. In order to ease the reading of the results, the water content was also drawn in function of vapor pressure instead of the relative humidity in Fig. 5.

Whatever the tested material, results underlines a good correlation between the predicted curves and the experimental data.
Fig. 4

Comparison between the measured and the calculated sorption curves at 10 and 40 °C for the earth plaster P1 (a) and the compacted earth C1 (b)

Fig. 5

Comparison between the measured and the calculated relation between the water content and the vapor pressure at 10 and 40 °C for the earth plaster P1 (a) and the compacted earth C1 (b)

4 Sorption curve and pore size distribution

4.1 Theoretical background

One other way to assess the evolution of sorption curves is the analysis of the mechanical equilibrium of the liquid–gas interface, which can be depicted by the Young-Laplace law:
$$\begin{aligned} P_{\rm atm}- P_{\rm L}= \gamma _{\text{L}, \text{G}} \kappa _{\text{L}, \text{G}} \end{aligned}$$
where \(P_{\rm atm}\) is the atmospheric pressure, \(P_{\rm L}\) is the liquid pressure, \(\kappa _{\rm L, G}\) is the average curvature of the liquid–gas interface and \(\gamma _{\text{L}, \text{G}}\) is the apparent surface tension between the liquid water and the in-pore gas. It is quite difficult to assess this latter since its value may be modified by the interactions between the water molecules and the pore walls. In this study, the assumption was made that the tabulated expression determined for pure unconfined water, that is \(\gamma _{\text{L}, \text{G}} =72.74 - 0.1513 (T-293.13)\) in [mN/m] [19], can be used.
If the deformation of in-pore space (due to mechanical loading or thermal dilation for example) and hysteresis phenomena are ignored, \(\kappa _{\text{L}, \text{G}}\) can directly be linked to the morphology of the porous network. This link has been already widely used in order to estimate the pore size distribution of porous material from their sorption/desorption curves [20, 21]. Under this strong assumption, which should however be checked, in particular for earthen materials with a high content in vegetal fibres (like straw or hemp), \(\kappa _{\text{L}, \text{G}}\) can be written in the form:
$$\begin{aligned} \kappa _{\text{L}, \text{G}} = \mathcal {F}^{-1} (w) \end{aligned}$$
where \(\mathcal {F}^{-1}\) is a monotonous bijective decreasing function of the water content, denoted by w, which satisfies \(\mathcal {F}^{-1}(w_\mathrm{sat}) = 0\), with \(w_\mathrm{sat}\) being the water content at saturation.
Alternatively, the chemical equilibrium between the adsorbed water and its vapor leads to the celebrated Kelvin’s law:
$$\begin{aligned} P_{\rm L}- P_{\rm atm}= \frac{\rho _{\rm L}RT}{M_{\text{H}_{2}\text{O}}} \ln \varphi \end{aligned}$$
where \(\rho _{\rm L}\) is the density of water, R is the perfect gas constant, \(M_{\text{H}_{2}\text{O}}\) is the molar mass of water, while T and \(\varphi\) are the temperature and the relative humidity at the local sorption/desorption front.
The combined use of (12), (10), and (11) allows to write ω in the form:
$$\begin{aligned} w(\varphi ,T) = \mathcal {F} \left( \frac{P_{\rm atm}-P_{\rm L}}{\gamma _{\text{L}, \text{G}}}\right) = \mathcal {F} \left( X \right) \end{aligned}$$
where \(\mathcal {F}\) is the inverse function of \(\mathcal {F}^{-1}\), and
$$\begin{aligned} X= \frac{-\rho _{\rm L}RT}{\gamma _{\text{L},\text{G}} M_{\text{H}_{2}\text{O}}} \ln \varphi \end{aligned}$$
The existence of this monotonous bijective function \(\mathcal {F}\) between the water content and X have been checked for the earth plaster P1 and the compacted earth C1 using the DVS’s sorption curves at 23 and 30 °C as well as the desiccator’s sorption curves at 10, 23 and 40 °C. The results are reported in the Fig. 6. They lead to quite consistent results, which tends to validate the existence of this function, at least for the tested materials.
Fig. 6

Relation between the water content and X for the earth plaster P1 and the compacted earth C1 from the sorption curves obtained at 10, 23 and 40 °C

Using this formalism, and assuming that the surface tension only depends on temperature, the variation of the water content with temperature at constant hygrometry can be linked to the slope of the isothermal sorption curve through the equation (proof in “Appendix”):
$$\begin{aligned} \frac{\partial w}{\partial T}(T,\varphi ) = \varphi \ln \varphi \left( \frac{1}{T} - \frac{\text{d}\ln \gamma _{\text{L},\text{G}}}{\text{d}T}\right) \xi (T,\varphi ) \end{aligned}$$
$$\begin{aligned} \xi (T,\varphi ) = \frac{\partial w}{\partial \varphi }(T,\varphi ) \end{aligned}$$
is the slope of the sorption curve at the temperature T for the relative humidity \(\varphi\).

4.2 Interface method: Variation of water content with temperature at constant relative humidity

Similarly to what it is done in the previous section, the Eq. (15) is used to estimate the variation of water content at constant humidity between 10 and 40 °C for the compacted earth C1 and the plaster P1:
$$\begin{aligned}&w(\varphi ,T_2)-w(\varphi ,T_1)\nonumber \\&\quad = \varphi \ln \varphi \left( \frac{T_2-T_1}{T_1}-\ln \left( \frac{\gamma _\mathrm{L,G}(T_2)}{\gamma _\mathrm{L,G}(T_1)}\right) \right) \xi (\varphi ,T_1) \end{aligned}$$
Throughout the rest of the paper, this way to estimate the variation of sorption curve with temperature is called the “interface method”.

The results, using the sorption curve at 23 °C obtained with the DVS as the reference curve, are showed in Fig. 5. They underline a good correlation between the experimental data and calculated values for earth plaster P1 and compacted earth C1 for the sorption curves at 10 and 40 °C.

5 Discussion

Both methods (either isosteric or interface) seem to quite well predict the variation of the sorption curve with temperature of the earthen materials tested in this study. However, information which is given by these two methods is intrinsically different. Isosteric method provides the variation of equilibrium relative humidity with temperature at constant water content while interface method gives the variation of water content with temperature at constant relative humidity.

Hygroscopic and hygrothermal models are based on the mass conservation of the in-pore water (both adsorbed, liquid and vapor). Assuming the equilibrium between all the in-pore water phases, and if the mass variation of vapor is strongly negligible towards the mass variation of liquid and adsorbed water, it leads to:
$$\begin{aligned} \rho _\mathrm{d} \frac{\partial w}{\partial t} = - \underline{\nabla } \cdot \left( \underline{g}_{\rm L}+ \underline{g}_{\rm v}\right) \end{aligned}$$
where \(\underline{g}_{\rm L}\) is the mass flow vector of liquid water, which depends on liquid pressure gradient and gravity through the Darcy’s law and \(\underline{g}_{\rm v}\) is the mass flow vector of vapor, which is composed by a diffusive term and an advective term, and which depend on gradients of vapor and total gas pressures. The developed equation of this relation can be found in a quite large amount of references, see for example [5, 22, 23]. Since the water content is a function of temperature and relative humidity, the first term of the Eq. (18), can be written as:
$$\begin{aligned} \rho _\mathrm{d} \frac{\partial w}{\partial t}=\rho _\mathrm{d} \left( \xi \frac{\partial \varphi }{\partial t}+\frac{\partial w}{\partial T} \frac{\partial T}{\partial t}\right) \end{aligned}$$
It follows that, to solve the Eq. (18), the information provided by the interface method is more convenient since it directly gives the term \(\partial w/\partial T\), and the combination between (15) and (19) provides:
$$\begin{aligned} \frac{\partial w}{\partial t} = \xi (T,\varphi ) \left( \frac{\partial \varphi }{\partial t}+ \varphi \ln \varphi \left( \frac{1}{T} - \frac{\text{d}\ln \gamma _{\text{L},\text{G}}}{\text{d}T}\right) \frac{\partial T}{\partial t} \right) \end{aligned}$$
What’s more, the knowledge of the function \(\mathcal {F}(X)\), which can be experimentally obtained by plotting ω as a function of \(X=\) \((-\rho _{\rm L}RT)/(\gamma _{\text{L},\text{G}} M_{\text{H}_{2}\text{O}} \varphi )\), would allow to assess the expression of \(\xi\) for each relative humidity and temperature through the Eq. (32) in “Appendix”. In consequence, under the assumptions and conditions of this study, only a single sorption curve is required to assess the evolution of water content with both temperature and relative humidity.

However, the interface method is based on the empirical knowledge of the \(\gamma _\mathrm{L,G}(T)\) function. Thus, for each new material, the existence of a function \(\gamma _\mathrm{L,G}(T)\) which allow to reach a single \(w=\mathcal {F}(X)\) curve must be verified. Along the same line, the assumption that \(\Delta h_\mathrm{v} = \Delta \dot{h}\) used in the isosteric method must be verified for each new tested material, especially when strong interactions may occurs between the adsorbed layer and the solid particles that forms the material.

Having said that, if the interface method is validated, the Eq. (20) can be used in order to estimate the impact of the temperature variation of the sorption curve on hygroscopic (and thus hygrothermal) calculations. For that purpose, the data from the Handbook of Chemistry and Physics [19], \(\text{d}\ln \gamma _{\text{L},\text{G}}/\text{d}T \approx - 2.6 \times 10^{-3}\) for temperature ranging from 0 and 50 °C is considered. This gives values of \(\varphi \ln \varphi \left( \frac{1}{T} - \frac{\text{d}\ln \gamma _{\text{L},\text{G}}}{\text{d}T}\right)\) which remain at most on the order of \(2 \times 10^{-3}\) \(\hbox {K}^{-1}\) (cf. Fig. 7). As a consequence, a 5 °C variation in temperature appears to have the same impact on the water content as a 1% variation in relative humidity, which is negligible. On the other side, for temperature variations higher than 25 °C, the variation of water content with temperature at constant humidity can become on the same order than a 5% variation in relative humidity, which may become significant.
Fig. 7

Evolution of the factor \(\varphi \ln \varphi \left( \frac{1}{T} - \frac{\text{d}\ln \gamma _{\text{L},\text{G}}}{\text{d}T}\right)\) with relative humidity and temperature

6 Conclusion

This paper presents a study on the impact of temperature on the sorption curves of earth plasters and compacted earth samples. For that purpose, two means of measurement are used, either the DVS (dynamic gravimetric sorption method) or the desiccator and saline solutions method (defined in the international standard ISO 12571 [24]). A good consistency was found between these two methods providing that the sample dry masses were determined using a similar protocol.

The prediction of sorption curves at several temperatures was made following two approaches. The first one, denoted by the “Isosteric method” was based on the well known Clapeyron relation. For that purpose, assuming that entropy of adsorbed water only depends on temperature, a simple expression of the latent heat of desorption was proposed. This method provides the variation of the equilibrium relative humidity with temperature at constant water content.

The second one, denoted by the “interface method”, gives variation of water content with temperature at constant relative humidity. It relies on the assumption of existence of a bijective function between the water content and the curvature of liquid–gas interface, which is in turn bijectively linked to the porous network geometry.

The sorption curves estimated with these two methods were quite similar and were consistent with the experimental data in the studied range of temperature (between 10 and 40 °C). This first result is quite interesting since it underlines that it is possible to predict the evolution of water content curve with temperature from the sole knowledge of one isothermal sorption curve.

Finally, using the interface method, the comparative impact assessment of temperature and relative humidity on water content have been realized. It follows that if temperature variations are below 25 °C, the induced variation in water content would be, at maximum, in the same range than the one induced by a 5% variation in relative humidity. Thus even if the choice of taking into account the temperature dependency of sorption curves will depend on the required precision, the assumption that \(w =w(\varphi )\) seems quite acceptable for moderate variations of temperature. Therefore, this study provides a simple tool which can assist in making that decision.

To conclude, even if the developments of this paper focuses on earthen materials submitted to quite moderate variations of temperature (realistic for the indoor atmosphere), the methodology which is developed may be applied to other materials and/or conditions. In that view, it may be interesting to analyze materials for which the sorption curve exhibits stronger dependency in temperature and/or for larger ranges of temperatures.



This present work has been supported by the French national research agency ANR, though the project BioTerra (ANR-13-VBDU-0005) and has received funding from the People Program (Marie Curie Actions) of the European Unions Seventh Framework Program (FP7/2007-2013) under REA grant agreement PCOFUND-GA-2013-609102, through the PRESTIGE program coordinated by Campus France. The authors are indebted to Joao Rodrigues Ferreira for its participation in the former experimentations on this subject during its internship at the ENTPE (from March to August 2016).

Compliance with ethical standards

Conflicts of interest

The authors declare that they have no conflict of interest.


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© RILEM 2017

This article is distributed under the terms of the Creative Commons Attribution 4.0 International License (, which permits unrestricted use, distribution, and reproduction in any medium, provided you give appropriate credit to the original author(s) and the source, provide a link to the Creative Commons license, and indicate if changes were made.

Authors and Affiliations

  1. 1.LTDS-LGCB, UMR 5513 CNRS, ENTPEUniversité de LyonVaulx-en-VelinFrance
  2. 2.CERIS and Department of Civil EngineeringNOVA University of LisbonCaparicaPortugal

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