Modeling PressureViscosity Behavior of OilBased Drilling Fluids
Modélisation du comportement pressionviscosité des fluides de forage à base d’huile
Facultad de Ciencias Experimentales, Departamento de Ingeniería Química, Centro de Investigación de Tecnología de Productos y Procesos Químicos (Pro 2TecS), Universidad de Huelva, Campus del Carmen, 21071
Huelva – Spain
email: martinez@uhu.es
^{*} Corresponding author
Received:
9
January
2017
Accepted:
4
May
2017
Organoclay suspensions are commonly used as drilling fluids in environments where they are submitted to high pressure and temperature for long periods of time. Consequently, both volumetric and thermorheological properties are among their most important quality parameters concerning this application. The overall objective of this work was to study the pressure and temperature dependence of both viscosity and density for oilbased drilling fluids. With this aim, PressureDensityTemperature (PρT) data and pressureviscositytemperature data were modeled by using different equations. All these equations predict the evolution of the viscosity of drilling fluids with pressure and temperature, for engineering purposes, fairly well.
Résumé
Les suspensions d’organoargiles sont couramment utilisées comme fluides de forage dans des environnements où elles sont soumises à des pressions et des températures élevées pendant de longues périodes. Par conséquent, les propriétés volumétriques et thermorhéologiques sont parmi les paramètres de qualité les plus importants pour ce type d’application. L’objectif général de ce travail était d’étudier la dépendance de la viscosité et de la densité en fonction de la pression et de la température des boues de forage à base d’huile. Dans ce but, les données de pressiondensitétempérature (PρT) et de pressionviscositétempérature ont été modélisées en utilisant différentes équations. Toutes ces équations prédisent assez bien l’évolution de la viscosité des fluides de forage en fonction de la pression et de la température, à des fins d’ingénierie.
© J. Hermoso et al., published by IFP Energies nouvelles, 2017
This is an Open Access article distributed under the terms of the Creative Commons Attribution License (http://creativecommons.org/licenses/by/4.0), which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.
Introduction
Organoclay suspensions are commonly used as oilbased drilling fluids due to their capacity to form gels and their suitable viscous properties. These fluids are submitted to high pressure and temperature in the well during drilling operations. The successful completion of an oil well and its cost depend, on a considerable extent, on the properties of these fluids [1, 2]. Hence, one of the most interesting points for the drilling industry is to develop fluid formulations, using new nanoscale additives [3, 4], in order to improve their thermophysical properties. Both, viscosity and density have been the two most extensively studied properties of organoclay dispersions used as drilling fluids. When drilling fluids are pumped down, they experience compression and expansion effects related to the increase or decrease of temperature and pressure along the wellbore. Density variations might be significant and its control is a challenging goal to minimize associated risks, and improve security and efficiency, particularly for oily systems [57]. Several authors have investigated the combined influence of pressure and temperature on the density of drilling fluids [811] However, few papers have been focused on the characterization of the PressureVolumeTemperature (PVT) relationship for this type of dispersions [12, 13].
In addition, the rheological behavior of oil drilling fluids is a critical issue in the success of drilling operations. Data concerning the influence of high pressure and temperature on the viscous properties of these types of suspensions are relatively scarce [14, 15]. However, knowledge of the flow behavior of claybased drilling fluids, as a function of temperature and pressure, is of a paramount importance in order to solve different important issues, such as excessive torque, gelation, hole cleaning, etc. [16].
Modeling the thermopiezoviscous behavior of fluids is a relevant issue for engineering applications involving processes at high pressure and temperature [17, 18]. In this sense, different equations based on the friction theory [19], the freevolume concept [20, 21], and empirical correlations [22] have been proposed to model the combined effect of temperature and pressure on the rheological properties of materials.
The overall objective of this work was to study the influence of pressure and temperature on viscosity and density of model oilbased drilling fluids. With this aim, PressureDensityTemperature (PρT) data were used to model the volumetric properties of the drilling fluids, by using Equation of State (EoS). Finally, using rheological, PVT, and calorimetric data, the pressuretemperatureviscosity behavior of these suspensions was modeled using different equations, such as FillersMoonanTschoegl’s (FMT), Yasutomi’s, and WLFBarus’ models.
1 Experimental
1.1 Materials
Two commercially available organoclays, denoted as B34 and B128 and provided by Elementis (Belgium), were used in the present study.
A mineral based lubricating oil, SR10 (0.916 g cm^{−3} at 40 °C) supplied by Verkol (Spain), was used as base oil for the formulation of the model oilbased drilling fluids.
1.2 Preparation of Organoclay Dispersions
Oil drilling fluids were prepared by mixing the organoclay (5% wt.) in SR10 oil base, using a high mixer Ultraturrax (Ika, Germany), at room temperature, at 9000 rpm for 5 min. Prior to its high shear processing, the organoclay was wetted with the oil for 1 h at room temperature.
1.3 Density Measurements
Two vibrating tube densimeters were used to measure the density, ρ, of the samples studied. At atmospheric pressure, an Anton Paar DMA 5000 (Austria) was employed to measure the density of SR10 oil and organoclay dispersions between 40 °C and 100 °C. Prior to performing density measurements with oil and organoclay dispersions at atmospheric pressure, the DMA 5000 densimeter was calibrated, as function of temperature, using both dry air and degasified bidistilled water as recommended by the manufacturer. The results obtained were compared with the values reported in Anton Paar’s manual for air and water in the temperature range used. For this densimeter, the manufacturer cited an uncertainty for temperature of ±0.01 °C, and density of ±5 × 10^{−6} g cm^{−3}, between 0 °C and 100 °C.
An Anton Paar DMA HPM highpressure vibrating tube (Austria) was used to measure the density in the temperature range comprised between 40 °C and 140 °C, and pressures up to 1200 bar. The temperature of the highpressure vibrating tube was controlled by an external circulating bath using silicone. The temperature was maintained constant within ±0.01 °C. A manual piston intensifier (HiP, USA) was used to control the pressure of the system. The pressure applied was measured by a pressure transducer model HP2S (Wika, Germany) with an uncertainty of less than 0.5% between 0 and 1600 bar.
The calibration of the HPM vibrating cell, in the entire range of pressure and temperature analyzed, was performed by using a polynomial expression as a function of temperature, pressure, and oscillation period given by Anton Paar:(1)where, ρ is the density of the fluid in g cm^{−3}, T the measured temperature in °C, P is the pressure applied in bar, τ is the oscillation period in ms, and FA_{i} the coefficients of the highpressure densimeter. These coefficients were evaluated by nonlinear regression of Equation (1) to standard densities for both dodecane [23] and water [24].
Taking into account the accuracies of temperature, pressure, period of oscillation, water and dodecane densities, and Equation (1) fitting for the reference fluids (0.07% for water and 0.1% for dodecane), the overall experimental uncertainty in oil and model oilbased drilling fluid densities is estimated to be ±1 × 10^{−3} g cm^{−3}. This uncertainty is similar to that previously reported in the literature [25].
1.4 Rheological Measurements
Viscous flow measurements were performed using a controlled stress rheometer, MARS II from Thermo Scientific (Germany). Rheological data were obtained using different geometries: a conventional coaxial cylinder geometry (41 mm inner diameter, 1 mm gap, 60 mm length) and a serrated plateandplate geometry (35 mm diameter, 1 mm gap) for rheological tests at atmospheric pressure; a coaxial cylinder geometry (38 mm diameter, 80 mm length) and a Double Helical Ribbon (DHR) geometry (36 mm diameter, 78 mm length), coupled with a pressure cell (D400/200), for measurements at high pressure. DHR is a nonconventional geometry, calibrated with a Newtonian fluid and several shearthinning fluids, in the pressure range used in the present study [26]. The cell D400/200 is a pressure vessel of 39 mm inner diameter. Inside the cell, the coaxial cylinder and the DHR geometry were put in contact with a sapphire surface, at the bottom of the vessel, by a steel needle. The inner geometry was equipped, at the top, with a secondary magnetic cylinder (36 mm diameter, 8 mm length), magnetically coupled to a tool outside the cell, which was connected to the motortransducer of the rheometer. The pressure cell was connected to a hydraulic pressurization system, which consists of two units, a high pressure valve and a hand pump (Enerpac, USA), connected by a high pressure line. The pressure cell was pressurized using, as pressurizing liquid, the same fluid to be tested. A pressure transducer GMH 3110 (Gresingeg Electronic, Germany), able to measure differential pressures ranging from 0 to 400 bar (0.1 bar resolution), was used.
Steadystate viscosity measurements, at different differential pressures (0, 100, 200, 300 and 390 bar) and temperatures (40, 80, 100, 120 and 140 °C), were performed in a shear rate range dependent on sample viscosity. The temperature in the high pressure cell was regulated with circulating silicone bath (DC30 Thermo Scientific, Germany), with an uncertainty of ±0.1 °C.
1.5 Differential Scanning Calorimetry
Differential Scanning Calorimetry (DSC) tests were carried out with a DSCQ100 calorimeter (TA Instruments, USA), using 510 mg samples sealed in hermetic aluminium pans. The sample was purged with dry nitrogen at a flow rate of 50 mL/min, to avoid any condensation of moisture. First, the pans where placed onto the cell at room temperature, then were heated at 80 °C, kept at this temperature for 5 min to reach the thermodynamic equilibrium, and subsequently, the samples were quenchedcooled to −80 °C, at 10 °C/min, kept for 5 min at this temperature to reach the equilibrium, and, finally, heated, at 10 °C/min, up to 180 °C. The glass transition temperature was determined from the inflection point of the steplike decrease in the heat flow.
2 Results and Discussion
2.1 Viscous Flow Behavior
Figures 1a and 1b show the steadystate viscous flow curves of the samples studied (SR10 oil, and B34 and B128based oily fluids), at 80 °C and pressures of 1 and 390 bar respectively. In the case of the oily suspensions, the steadystate viscous flow curves were obtained after upward and downward shear stress sweep tests, as has been described by the authors elsewhere [27, 28].
Figure 1
Experimental steadystate viscous flow curves, and Bingham’s model fitting, for SR10 oil, B34 and B128based drilling fluids (T = 80 °C; a) P = 1 bar; b) P = 390 bar). 
As can be observed in Figure 1, the viscous behavior of the SR10 oil is Newtonian in the pressure range of 1390 bar, at 80 °C. This oil also behaves as a Newtonian liquid for the whole range of temperature tested (40140 °C). In contrast, oil drilling fluids show a shearthinning behavior, exhibiting a Binghamlaw dependence of viscosity with shear rate in the whole range of pressure and temperature tested (1390 bar; 40140 °C), as has been previously reported [29, 30].
The Newtonian viscosity of the SR10 oil sample increases up to 2.13 times from atmospheric pressure to 390 bar, at 80 °C. However, the viscositypressure relationship for the drilling fluids is more complex, depending on both bentonite nature and shear rate. For example, the plastic viscosity increases ~2.11 times for B34 sample and ~2.22 times for B128 sample, in the abovementioned range of pressure. Nevertheless, at a shear rate of 1 s^{−1}, the plastic viscosity increases ~2.68 times for B34 sample and ~1.34 times for B128 sample. This complex piezoviscous behavior has been related to the development of complex molecular structures with different sensitivities to pressure and shear rate [29].
The thermopiezoviscous behavior of these materials can be modeled using equations developed for thermopiezorheologically simple materials, such as the FMT [30] the Yasutomi [31] or the empirical WLFBarus factorial model [27]. The approach is based on selecting characteristic rheological parameters, such as the Newtonian viscosity, in the case of the SR10 oil, or the plastic viscosity (η_{p}) of the model drilling fluids, to eliminate the complex shearrate dependence of the piezoviscous behavior, fitting the model equations to these selected shearrate independent parameters.
Viscositypressuretemperature models can be also classified as either only based on empirical parameters or based on some physical properties. Thus, the FMT model takes into account the pressure dependence of the bulk modulus and the expansivity. The pressure dependence of these properties can be obtained from the evolution of the density with pressure and temperature using the Murnaghan EoS. The Yasutomi model is described as a function of the glass transition temperature, which can be obtained from DSC measurements. The WLFBarus model describes the thermopiezoviscous behavior using empirical parameters for both temperature and pressure. To apply either FMT’s or Yasutomi’s model based on physical properties, the bulk modulus or the glass transition temperature should be previously determined by additional experiments.
2.2 DensityPressureTemperature Behavior
Figures 24 show the values of the density for the different samples studied, as a function of pressure (11200 bar) and temperature (40 °C up to 140 °C). As expected, a nearly linear decrease in density with temperature is observed for all samples in the range of temperature studied. Temperature and pressure exert an opposite influence on the volumetric behavior. The decrease in density when temperature is raised from 40 °C to 140 °C is compensated by an increase in pressure from 1 to ~1056 bar, for the SR10 oil and even slightly higher for both oilbased drilling fluids (up to ~1105 and ~1060 for B34 and B128, respectively). Thus, the influence of temperature is more relevant as compared to that of pressure. On the basis of this analysis, both model drilling fluids, B34 and B128, are slightly more susceptible to temperature than the base oil, showing the B34based drilling fluid the lowest susceptibility to pressure, at 140 °C. These drilling fluids show quite similar temperature susceptibility to that of the synthetic oilbased drilling fluids studied at low pressure [6]. On the contrary, these fluids show higher temperature susceptibility than those studied at high pressure [9].
Figure 2
Experimental density values, and Murnaghan’s equation fitting, for SR10 oil, as a function of pressure and temperature. 
Figure 3
Experimental density values, and Murnaghan’s equation fitting, for B34based drilling fluid, as a function of pressure and temperature. 
Figure 4
Experimental density values, and Murnaghan’s equation fitting, for B128based drilling fluid, as a function of pressure and temperature. 
The experimental evolution of the density, ρ, with both temperature and pressure can be described by the Murnaghan equation [32]:(2)being(3)
The polynomial function, ρ_{0}(0, T), represents the evolution of the density, at the reference pressure, where T_{ref} is the reference temperature (80 °C) and a_{0}, a_{1}, a_{2}, and a_{3} are fitting parameters, whose values, for the samples studied, are presented in Table 1. K_{e}(T) represents the temperature dependence of the bulk modulus of the entire volume, being the bulk modulus at zero pressure and temperature of reference; k_{e} is an empirical constant, the Bridgman constant, that implies a linear dependence of the bulk modulus with pressure [21]; and λ defines the temperature dependence of the bulk modulus at any given pressure [33] (, being m an empirical constant and the thermal expansivity of the entire volume at zero pressure and temperature of reference). The values of , k_{e} and λ are also presented in Table 1.
Murnaghan’s equation fitting parameters of PVT data modeling for the samples studied.
As can be seen in Figures 24, the Murnaghan equation describes the density evolution in the range of temperature and pressure studied fairly well. This equation has been extensively used by other authors to fit data of volumetric properties, as a function of temperature and pressure, of rubbery polymers [33] and heavy petroleum fractions [34]. For these samples, the values of the Percent Average Absolute Relative Deviation (%AARD), shown in Table 1, are lower than 0.07, indicating that this model is suitable for oilbased drilling fluids.
The evolution of the bulk modulus of the entire volume, K_{e}, with pressure, at the reference temperature (80 °C), is shown in Figure 5. The Murnaghan equation predicts a linear increase of the bulk modulus with pressure, as follows:(5)
Figure 5
Evolution of the entire bulk modulus for SR10 oil, B34 and B128based drilling fluids, as function of pressure, at 80 °C. 
In the range of pressure tested, both oil and drilling fluids show a qualitatively similar linear increase in the bulk modulus with pressure. This fact suggests that the volumepressure behavior for these fluids is determined by that of the base oil, as has been pointed out by other authors [10]. The values of the bulk modulus, calculated from PVT data, at 1 bar and 80 °C, are similar and slightly higher than those obtained for nparaffinic based drilling fluids [6] and mineral oilbased mud [8, 9] respectively, being the pressure susceptibility slightly higher for the samples studied.
The evolution of the expansivity, α_{e}(P), at constant temperature (80 °C), for the oil and oilbased drilling fluids studied is shown in Figure 6. A decrease in the expansivity values with pressure is observed for all the samples. According to the Murnaghan EoS, the isothermal expansivity can be described as follows:(6)
Figure 6
Evolution of the thermal expansivity for SR10 oil and oilbased drilling fluids, as a function of pressure, at 80 °C. 
Values for both the expansivity of the entire volume, , and the empirical parameter, m, are also presented in Table 1. As can be observed, the model drilling fluids present expansivity values at zero pressure slightly higher than the SR10 oil, more significantly for B34based drilling fluid, indicating that these suspensions are more compressible than the base oils. This fact suggests an increase in the free volume fraction of the suspension due to interactions between the oil and the organic chains of the organobentonite. Nevertheless, this effect vanishes as pressure increases, being the expansivities of the oil drilling fluids similar to that of the base oil at 400 bar, and even lower at higher pressures. These model drilling fluids show lower expansivity values than those formulated with mineral and vegetal oils [5].
2.3 TemperaturePressureViscosity Relationship
The FMT model has been successfully used for modeling the pressure and temperature dependence of heavy and intermediate fuel and recycled oils viscosities [3436]. Models based on molecular theories have the advantage of predicting the evolution of the rheological properties on the basis of the temperaturepressure evolution of some physical properties, such as expansivity and compressibility in the case of the FMT model. This model expresses the viscositypressuretemperature relationship as a function of molecular parameters:(7)being(8)
(15)where, η_{ref} is the viscosity at the reference temperature and pressure; f_{0} is the fractional freevolume at the reference temperature; B is a constant; α_{f}(P) is the expansivity of the freevolume, considered pressure dependent and temperature independent; is the expansivity of the free volume at zero pressure and temperature of reference, is the expansivity of the occupied volume at zero pressure and temperature of reference; are the bulk moduli of occupied volume, at zero pressure and temperature of reference; k_{ϕ} is the Bridgman constant for the occupied volume, the superscript 00 indicates temperature and pressure of reference.
With the coefficients , k_{e} and m determined from density measurements, the experimental viscosities can be used to determine the remaining parameters of the model (η_{ref}, B, f_{0}, k_{ϕ}, ), by fitting the set of Equations (7)(15), where η_{ref} depends on the temperature and pressure of reference, arbitrarily selected, and are constrained by the PVT behavior since . The values obtained for these parameters are shown in Table 2.
Values of the different FMT model parameters for the samples studied (T _{ref} = 80 °C; P _{ref} = 1 bar).
Among the models based on the freevolume concept, the Yasutomi model [37] has been extensively applied to model the pressuretemperatureviscosity relationship for polyethylene and different lubricant oils [38]. This model includes material properties at the glassy state:(16)where η_{g} is the viscosity at T_{g}, the glass transition temperature, which is a function of pressure:(17)and F is the free volume expansivity,(18a)being the expression for an improved definition [31]:(18b)where T_{g0} is the gas transition temperature at reference pressure; and c_{1}, c_{2}, A_{1}, A_{2}, B_{1} and B_{2} the parameters to be evaluated.
The range of pressure tested in this research is much narrower than that normally covered for lubricant studies [37]. Consequently, the viscositypressure evolution is simpler than that obtained for lubricant oils submitted to higher pressure. In these cases, the Yasutomi equation would be overparameterized, leading to several set of parameters from the regression procedure of the viscositypressure data. Consequently, in this fitting process, η_{g} and B_{2} have been arbitrarily set to 10^{12} Pa s and 1 respectively, using the T_{g0} values from DSC measurement as additional fixed parameters. The results obtained for the remaining parameters are shown in Table 3.
Values of the different parameters of the modified Yasutomi model for the samples studied (T _{ref} = 80 °C; P _{ref} = 1 bar).
Finally, the WLFBarus model combines two wellknown exponential equations, the WLF and a generalized version of the Barus equation, to describe both temperature and pressure effects on the viscosity:(19)where c_{1} and c_{2} are empirical constants. The piezoviscous coefficient, β_{s}, has been linearized with temperature in order to generalize the model. The results obtained from the application of the WLFBarus model to the viscosity data are shown in Table 4.
Values of the different parameters of the WLFBarus model for the samples studied (T _{ref} = 80 °C; P _{ref} = 1 bar).
Figure 7 shows the evolution with pressure of the Newtonian viscosity, for SR10 oil, and the plastic viscosity, for B34 and B128based oil drilling fluids, at the reference temperature (80 °C) as example. It can be seen that, at constant temperature, viscosity increases exponentially with pressure in the range of pressure tested. In addition, all the three models tested describe the isothermal evolution of viscosity with pressure, for engineering purposes, fairly well.
Figure 7
Experimental and estimated viscosities, using FMT, Yasutomi and WLFBarus models, for SR10 oil and drilling fluids, as a function of pressure, at 80 °C. 
In Figure 8, the experimental viscosity data (in the range 1400 bar and 40140 °C) of the samples studied and the calculated ones by using different models are compared (Fig. 8a: FMT’s model; Fig. 8b: Yasutomi’s model; and Fig. 8c: WLFBarus’ model). As can be seen, the largest deviations between experimental and calculated values are observed for B34 and B128 model drilling fluids, at 140 °C. These deviations, previously explained by the authors [27] are a consequence of the influence, on the rheological behavior of these drilling fluids, of the gelation process induced at high temperature. Excluding the results obtained at the abovementioned temperature (140 °C), the three models fit the experimental results, in the whole range of temperature and pressure tested, fairly well (average error less than 5%). Nevertheless, on the basis of the %AARD and relative deviation, each model behaves differently depending on the sample. Thus, both FMT’s and WLFBarus’ models show similar deviations and lower %AARD values for the SR10 oil (~2.3%, Tab. 24). B34 drilling fluid shows the highest values of %AARD and lowest R ^{2} correlation coefficient for any model tested, being WLFBarus’ model the best fit for this sample. On the contrary, Yasutomi’s model shows the lowest values of the %AARD for the B128 drilling fluid. The use of an empirical exponential function of temperature and pressure to model viscosity data of waterbased drilling fluids, oilbased drilling fluids [39] and invert oil mud [40, 41] is very common for engineering purposes, being the average error higher than those found in this research (around 5% [42] or even higher [43]).
Figure 8
Comparison of experimental and estimated viscosities by using a) FMT’s model; b) Yasutomi’s model and c) WLFBarus’ model. 
Conclusions
From the experimental results obtained, it can be concluded that model oilbased drilling fluid densities are more susceptible to changes in temperature than to pressure. The Murnaghan equation describes the PVT behavior, in the range of temperature and pressure studied, fairly well.
Different models can predict the evolution of the viscosity of drilling fluids with pressure and temperature. In this sense, freevolume models, based on physical parameters, do fit the viscositypressuretemperature data fairly well, showing similar or even lower error than some wellknown empirical exponential equations.
Acknowledgments
This work is part of a research project sponsored by a FEDER programme (research project CTQ201456980R). The authors gratefully acknowledge the financial support received.
References
 Khalil M., Mohamed Jan B. (2012) Viscoplastic modeling of a novel lightweight biopolymer drilling fluid for underbalanced drilling, Ind. Eng. Chem. Res. 51, 4056–4068. [Google Scholar]
 Zhou D., Zhang Z., Tang J., Wang F., Liao L. (2016) Applied properties of oilbased drilling fluids with montmorillonites modified by cationic and anionic surfactants, Appl. Clay Sci. 121122, 1–8. [Google Scholar]
 Halali M.A., Ghotbi C., Tahmasbi K., Ghazanfari M.H. (2016) The role of carbon nanotubes in improving thermal stability of polymeric fluids: Experimental and modeling, Ind. Eng. Chem. Res. 55, 7514–7534. [Google Scholar]
 Hilhorst J., Meester V., Groeneveld E., Dhont J.K., Lekkerkerker H.N. (2014) Structure and rheology of mixed suspensions of montmorillonite and silica nanoparticles, J. Phys. Chem. B 118, 11816–11825. [CrossRef] [PubMed] [Google Scholar]
 Hussein A.M.O., Amin R.A.M. (2010) Density measurement of vegetable and mineral based oil used in drilling fluids, SPE Nigeria Annual International Conference and Exhibition, 2010, 31 July7 August 2010, Calabar, Nigeria, SPE 136974,, pp. 237–242. [Google Scholar]
 Demirdal B., Miska S., Takach N., Cunha J.C. (2007) Drilling fluids rheological and volumetric characterization under downhole conditions, Proceedings of the SPE Latin American and Caribbean Petroleum Engineering Conference, 3, pp. 1616–1623. [Google Scholar]
 Kim N.R., Ribeiro P.R., PessôaFilho P.A. (2015) PVT behavior of methane and esterbased drilling emulsions, J. Petrol. Sci. Eng. 135, 360–636. [CrossRef] [Google Scholar]
 Peters E.J., Chenevert M.E., Zhang C. (1990) Model for predicting the density of oilbased muds at high pressures and temperatures, SPE Drill. Complet. 5, 141–148. [Google Scholar]
 Hemphill T., Isambourg P. (2005) New model predicts oil, synthetic mud densities, Oil Gas J. 103, 56–58. [Google Scholar]
 Demirdal B., Cunha J.C. (2009) Olefinbased syntheticdrillingfluids volumetric behaviour under downhole conditions, SPE Drill. Complet. 24, 239–248. [CrossRef] [Google Scholar]
 Hermoso J., MartínezBoza F.J., Gallegos C. (2017) Organoclay influence on high pressurehigh temperature volumetric properties of oilbased drilling fluids, J. Petrol. Sci. Eng. 151, 13–23. [CrossRef] [Google Scholar]
 Babu D.R. (1993) Effect of PρT behaviour of water muds on static pressures during deep well drilling, J. Petrol. Sci. Eng. 9, 341–439. [CrossRef] [Google Scholar]
 Zamora M., Roy S., Slater K.S., Troncoso J.C. (2013) Study on the volumetric behavior of base oils, brines, and drilling fluids under extreme temperatures and pressures, SPE Drill. Complet. 28, 278–288. [CrossRef] [Google Scholar]
 Gandelman R.A., Leal R.A.F., Gonyalves J.T., Aragao A.F.L., Lomba R.F., Martins A.L. (2007) Study on gelation and freezing phenomena of synthetic drilling fluids in ultradeep water environments, SPE/IADC Drilling Conference and Exhibition 2007, 20 February 2007, Amsterdam, Netherlands, Vol. 3, pp.1013–1020. [Google Scholar]
 Zhao S.Y., Yan J.N., Shu Y., Zhang H.X. (2008) Rheological properties of oilbased drilling fluids at high temperature and high pressure, J. Cent. South Univ. Technol. 15, 457–461. [CrossRef] [Google Scholar]
 Shahbazi K., Metha S.A., Moore R.G., Ursenbanch M.G., Fraassen K.C.V. (2007) Oxidation as a rheology modifier and a potential cause of explosions in oil and syntheticbased drilling fluids, SPE International Symposium on Oilfield Chemistry, Houston, TX, USA, pp. 157–165. [Google Scholar]
 Hron J., Málek J., Rajagopal K.R. (2001) Simple flows of fluids with pressuredependent viscosities, Proc. R. Soc. A 457, 1603–1622. [CrossRef] [Google Scholar]
 Franta M., Malek J., Rajagopal K.R. (2005) On steady flows of fluids with pressureandsheardependent viscosities, Proc. R. Soc. A 461, 651–670. [CrossRef] [Google Scholar]
 QuiñonesCisneros S.E., Deiters U.K. (2006) Generalization of the friction theory for viscosity modeling, J. Phys. Chem. B 110, 12820–12834. [CrossRef] [PubMed] [Google Scholar]
 Tschoegl N.W., Knauss W.G., Emri I. (2002) The effect of temperature and pressure on the mechanical properties of thermoand/or piezorheologically simple polymeric materials in thermodynamic equilibrium – A critical review, Mech. TimeDependent Mater. 6, 53–99. [CrossRef] [Google Scholar]
 Fillers R.W., Tschoegl N.W. (1977) Effect of pressure on the mechanical properties of polymers, Trans. Soc. Rheol. 21, 51–100. [CrossRef] [Google Scholar]
 Berthe D., Vergne P. (1990) High pressure rheology for high pressure lubrication: A review, J. Rheol. 34, 639–655. [CrossRef] [Google Scholar]
 Lemmon E.W., Huber M. (2004) Thermodynamic properties of ndodecane, Energy Fuels 18, 960–967. [Google Scholar]
 Wagner W., Pruβ A. (2002) The IAPWS formulation 1995 for the thermodynamic properties of ordinary water substance for general and scientific use, J. Phys. Chem. Ref. Data 31, 387–535. [Google Scholar]
 Dávila M.J., Alcalde R., Atilhan M., Aparicio S. (2012) PρT measurements and derived properties of liquid 1alkanols, J. Chem. Thermodyn. 47, 241–259. [Google Scholar]
 Hermoso J., Jofore B.D., MartínezBoza F.J., Gallegos C. (2012) High pressure mixing rheology of drilling fluids, Ind. Eng. Chem. Res. 51, 14399–14407. [Google Scholar]
 Hermoso J., MartínezBoza F.J., Gallegos C. (2014) Combined effect of pressure and temperature on the viscous behaviour of alloil drilling fluids, Oil Gas Sci. Technol – Rev. IFP 69, 1283–1296. [CrossRef] [EDP Sciences] [Google Scholar]
 MartínAlfonso M.J., MartínezBoza F.J., Partal P., Gallegos C. (2006) Influence of pressure and temperature on the flow behaviour of heavy fuel oils, Rheol. Acta 45, 357–365. [Google Scholar]
 Poling B.E., Prausnitz J.M., O’Connell J.P. (2001) The properties of gases and liquids, 5th edn., McGrawHill, New York. [Google Scholar]
 Moonan W.H., Tschoegl N.W. (1983) Effect of pressure on the mechanical properties of polymers. 2. Expansivity and compressibility measurements, Macromolecules 16, 55–59. [Google Scholar]
 Bair S., Mary C., Bouscharain N., Vergne P. (2013) An improved Yasutomi correlation for viscosity at high pressure, Proc. Inst. Mech. Eng. Part J 227, 1056–1060. [CrossRef] [Google Scholar]
 Murnaghan F.D. (1951) Finite deformation of an elastic solid, Wiley, New York. [Google Scholar]
 Fakhreddine Y.A., Zoller P. (1990) Equation of state of a polydimethylsiloxane fluid, J. Appl. Polym. Sci. 41, 1087–1093. [Google Scholar]
 MartínAlfonso M.J., MartínezBoza F.J., Navarro F.J., Fernández M., Gallegos C. (2007) Pressuretemperatureviscosity relationship for heavy petroleum fractions, Fuel 86, 227–233. [CrossRef] [Google Scholar]
 MartínezBoza F.J., MartínAlfonso M.J., Gallegos C., Fernández M. (2001) Highpressure behavior of intermediate fuel oils, Energy Fuels 25, 5138–5144. [Google Scholar]
 MartínezBoza F., FernandezLatorre F., Gallegos C. (2009) Highpressure viscosity of used motor oil/vacuum residue blends, Fuel 88, 1595–1601. [CrossRef] [Google Scholar]
 Yasutomi S., Bair S., Winer W.O. (1984) An application of a free volume model to lubricant rheology I – Dependence of viscosity on temperature and pressure, J. Tribol. 106, 291–302. [Google Scholar]
 Bair S. (2001) Highpressure highshear stress rheology of polybutene, J. NonNewtonian Fluid Mech. 97, 53–65. [CrossRef] [Google Scholar]
 Houwen O.H., Geehan T. (1986) Rheology of oilbase muds, SPE paper 15416 presented at the SPE Annual Technical Conference and Exhibition, 58 October, held in New Orleans, LA, USA. [Google Scholar]
 Politte M.D. (1985) Invert oil mud rheology as a function of temperature and pressure, SPE paper 13458 presented at the SPE/IADC Drilling Conference, 68 March, held in New Orleans, LA, USA. [Google Scholar]
 Hermoso J., MartínezBoza F.J., Gallegos C. (2015) Influence of aqueous phase volume fraction organoclay concentration and pressure on invertemulsion oil muds rheology, J. Ind. Eng. Chem. 22, 341–349. [CrossRef] [Google Scholar]
 Demirdal B., Cunha J.C. (2009) Importance of drilling fluids′ rheological and volumetric characterization to plan and optimize managed pressure drilling operation, J. Can. Petrol. Technol. 48, 8–14. [CrossRef] [Google Scholar]
 Santoyo E., García A., Morales J.M., Contreras E., EspinosaParedes G. (2001) Effective thermal conductivity of Mexican geothermal cementing systems in the temperature range from 28 °C to 200 °C, Appl. Thermal Eng. 21, 1799–1812. [CrossRef] [Google Scholar]
All Tables
Murnaghan’s equation fitting parameters of PVT data modeling for the samples studied.
Values of the different FMT model parameters for the samples studied (T _{ref} = 80 °C; P _{ref} = 1 bar).
Values of the different parameters of the modified Yasutomi model for the samples studied (T _{ref} = 80 °C; P _{ref} = 1 bar).
Values of the different parameters of the WLFBarus model for the samples studied (T _{ref} = 80 °C; P _{ref} = 1 bar).
All Figures
Figure 1
Experimental steadystate viscous flow curves, and Bingham’s model fitting, for SR10 oil, B34 and B128based drilling fluids (T = 80 °C; a) P = 1 bar; b) P = 390 bar). 

In the text 
Figure 2
Experimental density values, and Murnaghan’s equation fitting, for SR10 oil, as a function of pressure and temperature. 

In the text 
Figure 3
Experimental density values, and Murnaghan’s equation fitting, for B34based drilling fluid, as a function of pressure and temperature. 

In the text 
Figure 4
Experimental density values, and Murnaghan’s equation fitting, for B128based drilling fluid, as a function of pressure and temperature. 

In the text 
Figure 5
Evolution of the entire bulk modulus for SR10 oil, B34 and B128based drilling fluids, as function of pressure, at 80 °C. 

In the text 
Figure 6
Evolution of the thermal expansivity for SR10 oil and oilbased drilling fluids, as a function of pressure, at 80 °C. 

In the text 
Figure 7
Experimental and estimated viscosities, using FMT, Yasutomi and WLFBarus models, for SR10 oil and drilling fluids, as a function of pressure, at 80 °C. 

In the text 
Figure 8
Comparison of experimental and estimated viscosities by using a) FMT’s model; b) Yasutomi’s model and c) WLFBarus’ model. 

In the text 