Studying the role of fine materials characteristics on the packing density and rheological properties of blended cement pastes

In this investigation, standardized cement (CEM I 42.5N) according to EN 197-1 was adopted for all mixes. Additionally, several mineral admixtures are used as follows: class (F) fly ash with two levels of fineness: coarse (CFA) and fine (FFA); SL; SF; inert limestone powder with three levels of fineness: coarse (CLP), medium (MLP), and fine (FLP); and inert quartz powder with three levels of fineness: coarse (CQP), medium (MQP), and fine (FQP). All used materials were provided by Sika GMBH Company and comply with EN standards. In this study, materials with fineness in the range of cement are considered coarse, while materials with higher fineness are considered fine. The measured chemical composition and physical properties of the used fine materials are summarized in Table 1. The phase composition was examined using an X-ray diffractometer and is represented in Figure 1. Also, the PSD was measured by a laser diffraction analyzer, as shown in Figure 1. Typical scanning electron microscope (SEM) images for all mineral admixtures used in this study are given in Figure 2.

Figure 1

PSD of different mineral admixtures.

Figure 2

SEM images of the used fine materials.

To evaluate the influence of binary system composition on dense packing and the performance of fresh pastes, this investigation, in the first part, measured viscosity, fresh density, and PD of different cement-mineral admixture systems. To reveal the governing factors, binary systems were produced to evaluate the influence of mineral admixture type and dosage. The content of mineral admixtures in the binary system was selected based on the literature survey. Besides SF, which was implemented at a dosage rate of 3, 6, 9, 12, and 15 wt%, other mineral admixtures were implemented at rates of 10, 20, 30, 40, and 50 wt% of cement. In total, 51 different pastes were prepared and tested. The water/binder ratio for all mixes was kept constant at 0.35 to avoid its influence on the studied characteristics. Details of the mix proportions are shown in Table 2.

The main target of this research is to study the influence of fine material characteristics on PD and rheological properties of binary cement pastes. First, the characteristics of the used fine materials, including PSD, surface area, fineness, water demand, chemical composition, and SEM images, have been measured. The experimental work includes the measurement of PD using two methods: the De Larrard method and the centrifugal consolidation method. The reason for using two different methods is the absence of a standard testing method to measure PD. Additionally, the complex and random nature of particle behavior in the mixture makes the measurement of the PD of fine particles a challenging problem and a very complicated process. On the other hand, the slump flow test, shear stress, and viscosity were measured to assess the rheology of the fresh pastes. The density of fresh pastes has been measured to compare it with the results of PD.

3.3.3

Rheology

The rheological characteristics of cement pastes were determined using the Schleibinger Viskomat NT rotational rheometer with two hollow blade rotors, the dimensions and geometry of which are illustrated in the study by Haist et al. [32]. A rotational speed vs time protocol, as shown in Figure 5, was implemented for all cementitious systems, and the material response in terms of the moment of resistance for different pastes was recorded. A pre-shearing at a maximum rotational speed of 120 rpm was performed due to the thixotropic behavior of cement-based materials before the torque stabilized and the flow reached a steady-state condition [33]. Additionally, a step shear profile with consecutively lower rotational speeds of 80, 40, and 20 rpm was performed. For each step, the shear rate was held constant for a short period, and the equilibrium moment was recorded.

For the derivation of yield stress and plastic viscosity, the Couette inverse problem is frequently used, and the transformation is usually approximated using the Reiner–Riwlin equation, which assumes Bingham flow behavior [34]. An extension of the Reiner–Riwlin equation was proposed by Feys et al. to account for the general nonlinear relationship between shear stress and shear rate in cementitious systems [35]. However, these derivations are principally associated with co-axial cylinder rheometers and, therefore, their applicability for determining rheological parameters in the case of a two-hollow-blade rotor is unsupported. In addition, this difficulty is aggravated by the fact that, unlike other rotor geometries, the flow around the rotor is three-dimensional, and in the absence of a defined shear plane and flow boundary condition in terms of shear gradient, the pattern of the relationship between shear stress and shear rate may remain unknown. Based on the abovementioned, and for this study, the affine translation approach introduced in the study by Haist [32] for converting raw data into absolute rheological parameters was adopted (Figure 3). In this approach, reference was made to the absolute rheological parameters of ultrasound gel obtained using a cone plate rotor, to which a defined shear plane and shear gradient exist. The torque and rotational speed measurements were best fitted using linear regression for each geometry. Then, conversion factors were evaluated for the transformation of torque and rotational speed for arbitrary geometry into identical shear stress and shear rate determined using the cone plate assemblage by using affine translation. These conversion factors were subsequently utilized for the transformation of torque and rotational speed into yield stress and plastic viscosity using equations (2) and (3) for arbitrary geometrical configurations (Figure 4). (2) τ O , AT , C = A rheo × T OC , {\tau }_{\text{O},\text{AT},\text{C}}={A}_{\text{rheo}}\times {T}_{\text{OC}}, (3) μ AT , C = A rheo M rheo × S C × 60 2 π , {\mu }_{\text{AT},\text{C}}=\frac{{A}_{\text{rheo}}}{{M}_{\text{rheo}}}\times {S}_{\text{C}}\times \frac{60}{2\text{π}}, where T _{O, AT, C} is the absolute yield stress (Pa), μ _{AT, C} is the plastic viscosity (Pa s), T _OC is the yield torque (NM), Sc is the slope, and A _rheo and M _rheo are the conversion factors. For the two hollow blade rotors used in this investigation, Arheo and Mrheo were found equal to 2.16 Pa/N mm and 5.16 s⁻¹/rad⁻¹, respectively. Although there is no general validity of affine translation, it is admitted by the authors as the most reliable and accurate approach for processing the raw data of this study. Figure 5 illustrates the rheometer set up and procedure for determination of visco-elastic properties (a) Rotational speed vs time protocol and (b) moment of resistance of measurements for the control paste. The equilibrium moment was taken equal to the average moment for the last minute of each step (c) regression line for torque vs rotational speed and (d) conversion of torque and rotational speed measurements into shear stress and shear rate using affine translation (the intercept represents yield stress and the slope represents viscosity).

Figure 3

Measurement of flow spread of different cement pastes.

Figure 4

Schleibinger Viskomat NT to measure rheological characteristics.

Figure 5

Rheometer set up and procedure for determination of visco-elastic properties. (a) Rotational speed vs time protocol; (b) moment of resistance of measurements for the control paste; (c) regression line for torque vs rotational speed and (d) conversion of torque and rotational speed measurements into shear stress and shear rate using a ffine translation.

The results of the PD of the developed binary systems are given in Table 2 and are presented in Figures 6 and 7. The experimental results clarify that there are slight differences between the two measuring methods. The centrifugal consolidation method gives higher values for pure cement paste than De Larrard. For other mixes, the differences are not significant; particularly, both methods have the same trends to a large extent. The difference in the measured values could be due to the differences in the concept and measuring procedure, which can be affected by the input material characteristics. Both methods depend largely on PSD, particle shape, and mixture composition.

Figure 6

Packing densities of different pastes using De Larrard method.

Figure 7

Packing densities of different pastes using the Centrifugal method.

Based on the obtained results, it is clear that both methods can be applied in the construction materials technology field and are highly sensitive to changes in the content or characteristics of the used materials. From Figures 6 and 7, it is clearly demonstrated that the partial substitution of cement with mineral admixtures increases the PD due to the excessive filling effect. Cement alone has relatively poor PD owing to its narrow PSD, which increases the voids between the particles. The use of fine materials with different sizes from cement significantly decreases the voids in the cementitious material system, depending on the fineness and shape of the particles. In general, high packing can be obtained when particles with a broader range of sizes are incorporated due to the successive filling process. The experimental results show that CFA and FFA yield increments of 9.5 and 7.5%, respectively, at a replacement ratio of 50% compared to the control mix. The spherical shape of FA particles, as indicated in SEM graphs, results in a reduction of inter-particle forces, thus allowing for better packing. The influence of CFA with coarser PSD on packing is more pronounced in comparison to the finer PSD of FFA. Regarding all tested materials, CLP has the highest PD. When compared to other limestone powders at a replacement ratio of 50%, CLP, MLP, and FLP enhance the PD by 10.4, 5.6, and 4.3%, respectively. This observation complies with what was obtained for FA by Mehdipour and Khayat [36], who reported that a substantial increase in SSA can lead to a relative increase in inter-particle distance due to the loosening effect of fine materials, thus lowering the PD of the paste. Additionally, the wider PSD of CFA and CLP allows the smaller particles to fill the spaces between larger particles and increase the PD. The influence of silica fume on the PD of cement pastes is significant, with a major increase for mixtures with 3 and 15% SF, of 3.2 and 4.7%, respectively, compared to the mixture without SF. Further inclusion of SF decreases the PD due to the excessive content of finer particles and inadequate dispersion of SF in the paste [36]. Meanwhile, slag exhibited the lowest PD behavior due to particle shape and its similarity in PSD to ordinary portland cement (OPC), and therefore, the extent of the increase is negligible. CQP increases PD compared to MQP due to the broader PSD of the mixture. Regarding the influence of FQP on PD, there is an optimum content of 20% at which the densest packing was achieved; afterward, the addition of FQP resulted in a significant decrease of 2.5%. This is attributed to the mono-sized PSD rather than the multi-sized PSD, which, especially at high replacement dosages, can repel cement particles and lower the PD.

Broadly speaking, the effects of various materials on PD using centrifugal consolidation follow the same pattern as the De Larrard method. CFA and FFA increase the PD to 59.9 and 58.9%, respectively. SF also increases the PD at rates up to 12%; however, SF with high content, 15% significantly reduces PD. On the other hand, slag blends displayed no difference in PD measurements. This result implies that the influence of the PSD of mineral admixtures, rather than the morphology of particles, is dominant. CLP shows a perpetual increase that reaches a value of 59.7%. The favorable effect of CLP on packing was discussed earlier. In comparing LPs, both CLP and MLP show a soaring diagram over all used replacement ratios and attain values of 59.7 and 59.1%, respectively, at an LP dosage of 50%, whereas the PD of FLP escalates to 58.2% at a replacement ratio of 20%. Thereafter, the increase in PD with the increase in FLP content is negligible. A similar discussion can be made for CQP and MQP but with lower PD measurements of 58.3 and 57.9%, respectively. However, for FQP, as the content increases between 0 and 20%, there is an increase in PD by 1.3%, then the PD remains approximately the same before it eventually declines by 2.8% for mixture FQP50 due to the loosening effect of fine materials. SL and CQP approximately have a similar PSD; however, CLP50 gives a 2.1% increase in PD over SL50 as the angular morphology of SL lowers the packing of the constituent particles. The PD of any material depends mainly on the PSD, particle shape, and surface smoothness. For cement alone, the narrow PSD leads to a decrease in the filling process of particles with each other and results in poor packing. When fly ash is used, the PD increases significantly due to the wide range of particle sizes on one hand and the spherical shape of particles on the other hand. In contrast, when quartz powder and slag are used to partially substitute cement, the obtained PD decreases due to the edged shape of the particles, which increases the blocking between particles, increases the voids, and decreases the PD. The use of ultra-fine materials such as SF results in a significant increase in PD to a certain extent, while above the saturation point, it starts to decrease due to the occupying effect.

The flow spread results are shown in Figure 8. It is evident that CFA, CLP, MLP, and CQP improve flowability with increasing addition content due to the increase in PD. Comparing the flow spread of different pastes when the addition content reaches 50%, CLP, which has the highest PD, has the most favorable effect on flowability. Generally, CFA increases flowability in comparison with MLP. This could be attributed to the higher PD of CFA and the spherical geometry of its particles, which make it easier for the particles to roll against one another and improve flowability (ball bearing effect). When the fineness level of a material with a similar mineralogical composition increases, it negatively affects flowability, as manifested in FAs, LPs, and QPs. SF, although improving PD up to 12%, adversely affects the flowability of paste. Apart from the fact that increased PD increases excess water beyond that required to fill the voids between particles, the SSA governs the WFT necessary to coat the entire particle surface. Thus, for a similar amount of excess water, flowability is inversely proportional to the SSA.

Figure 8

Flow spread of different pastes including different mineral admixtures.

In order to investigate the influence of WFT on flow behavior, WFT over the particles was calculated. First, the ratio of excess water, which is the total water minus the water demand of the pastes, to the volume of solid particles was calculated. Then, WFT was computed as the ratio of the excess water to the SSA of the particles [27]. Figure 9 shows the flow spread of different pastes vs WFT. The water demand obtained from the centrifugal consolidation method was used in the calculation; however, a similar demonstration could be derived using the De Larrard method. For SL, LPs, and QPs, the flow increases linearly with the increase in WFT. The rate of increment in flow spread is 3.8 mm for each increment in WFT of 1 µm. However, this linear correlation between flow spread and WFT is not universal. For FAs and SF, the correlation between flow spread and WFT follows a parabolic form. The deviation from linearity for FAs and SF is mainly due to the sphericity and the replacement ratio. To illustrate this, the WFT for mixtures CFA10 and CFA20 is significant due to a higher PD and a lower SSA; however, the flow spread is reduced owing to the partial replacement of cement by only 10 and 20% with spherical FAs. Nevertheless, for irregularly shaped particles, the linear correlation remains valid, demonstrating that the flow spread is exclusively dependent on the WFT surrounding the particles. The influence of WFT on flow spread follows linear and quadratic trends for irregular and spherical particles, respectively, as presented in Figure 9. The linear curve for irregular particles demonstrates the negative effect of irregular shapes on flowability, requiring increasing amounts of water to reach the saturation point. However, for spherical particles, there is a certain WFT limit, above which the excess addition of water negatively influences flow spread. Generally, the flowability of the paste depends mainly on the mixture composition, the PD of the mixture, the characteristics of the used materials, and the w/b ratio. For the same water content, flowability increases with increasing PD (limestone powder mixes) due to the excess amount of water available to lubricate the particles and facilitate the movement. Additionally, particle shape and surface smoothness have a significant influence on flowability levels. Particles with irregular shapes (quartz powder and slag mixes) decrease flow values due to high friction between them, which requires external factors such as water-reducing admixtures or vibration forces to achieve the required flowability. In contrast, spherical particles (fly ash mixes) significantly increase paste flow at the same w/b ratio.

Figure 9

Flow spread of different pastes vs WFT.

The results of the fresh density of the mixtures are given in Table 2. For FA, SL, and SF, the effect of PD on fresh density cannot be readily established due to variations in specific density. However, in the case of LPs and QPs with similar specific gravity, the PD results in an increase in the fresh density of pastes with similar composition, which could be attributed to the increase in solid concentration and the reduction in voids in the system. Despite the crucial role of the particle density of the supplementary materials used in the fresh density of the pastes, other factors such as shape and fineness also play important roles. For example, SL has the highest particle density compared to other fine materials used, about 2.91; however, with partial substitution of cement, the fresh density decreases gradually. Similarly, fine quartz powder decreases the fresh density even though it has a high particle density. In contrast, CLP, with a particle density similar to that of quartz powder, exhibited fresh density values close to those of SL. This could be due to the high packing of limestone powder particles. Generally speaking, the fresh density and PD results agree to a certain extent, taking into account the particle density of the input materials. The density of any material depends mainly on the volumetric proportions of the solid structure to the void content. When spherical particles are used in combination with a wide distribution of particle sizes, the PD increases, and consequently, the paste density increases. On the contrary, when quartz powder with irregularly shaped particles is used, the PD decreases, the void content increases, and the paste density decreases.

Figure 10 shows the change in viscoelastic properties as a function of the additive content. For CFA, the yield stress and plastic viscosity continuously decrease with an increase in dosage percentage. This is believed to be attributed to the ball-bearing effect of the spherical and smooth surface of FA particles, which reduces inter-particle frictional forces and improves flowability. However, this behavior is not extrapolated to very FFA, especially with a high level of cement replacement. For FFA mixtures, both yield stress and plastic viscosity roughly decrease at a percentage of 10%, then increase again. Despite the spherical geometry of FFA, the increase in yield stress could be ascribed to the higher fineness of FFA particles. The inclusion of FFA improves PD, as shown in Figures 5 and 6, leading to the release of additional water due to the filling effect; however, this does not suffice to counterbalance the tremendous increase in SSA. Therefore, it cannot be employed in the lubrication of the mix, and as a consequence, a higher yield stress is observed. Concerning plastic viscosity, FFA increases the number of contact points and increases the plastic viscosity of the cementitious system.

Figure 10

Yield stress and plastic viscosity of cement pastes.

The inclusion of SF exceedingly increases the yield stress, and the rate of increase escalates with percentage addition. SF can fill the voids in the cementitious system and therefore increase the PD, specifically at lower doses. However, the water liberated does not suffice to cover the immense increase in surface area, leading to an overall decline in flowability. Additionally, SF remarkably decreases the plastic viscosity. A probable reason is that, in addition to the sphericity of particles, ultra-fine particles smaller than 0.3 mm intermingle with water to form a slurry film over larger particles. Therefore, slurry film thickness was introduced in investigating the properties of pastes incorporating ultra-fine materials. The addition of SF content, although giving rise to increased yield stress, results in a decreasing rate of shear stress increase once the flow begins. This occurs due to a larger WFT around particles, leading to lower plastic viscosity. For SF12 and SF15 mixes, after the structure is broken down and steady-state flow occurs, the torque measurements successively increase as rotational speed decreases, resulting in a negative value for plastic viscosity. This may be attributed to the high surface area of SF particles, which results in the structural rebuild of particles at lower rotational speeds and increases the torque resistance of the system. On the other hand, the addition of slag to the system results in a slight decline in flowability, as reflected by a modest increase in yield stress and plastic viscosity with increasing slag content. This is because slag particles have an angular shape and a lower ability to pack efficiently. Therefore, an insufficient amount of water is liberated from inter-particle voids, negatively influencing the rheology of the paste, as shown in Figures 7 and 8.

The effect of PD on the rheological properties of CLP-OPC systems is evident. As CLP particles tend to pack densely, they lead to an increase in WFT and have a favorable effect on yield stress and viscosity as a consequence. In the comparison of LPs with varying levels of fineness, CLP, followed by MLP, enhances the rheological behavior, whereas FLP has a negative effect. A similar general trend is observed for QPs. CQP diminishes yield stress and plastic viscosity, specifically for addition rates below 30%, whereas MQP and FQP increase yield stress and plastic viscosity. FQP adversely changes the rheology of the pastes compared to FLP and even SF. This is mainly attributed to the lower PD, as demonstrated earlier, coupled with the higher surface area of the material, which reduces the WFT and consequently decreases rheology. For SL and MQP, the two materials with similar PSD exhibit the same increasing trend in rheological parameters but at different rates. Although SL shows a lower PD, it has a favorable effect on yield stress and plastic viscosity compared to CQP, possibly due to the glassy surface of the particles. Similarly, SF, with its tiny particles and high fineness, has a significant influence on the measured plastic viscosity. On the other hand, coarse fly ash decreases the plastic viscosity of the pastes owing to the ball-bearing effect of its spherical particles.

To study the influence of WFT on rheology, the relationship between yield stress and WFT is given in Figure 11. It is clearly seen that an inverse linear relationship exists when yield stress and WFT are plotted on a logarithmic scale, indicating that yield stress increases at a progressively increasing rate as WFT decreases. Moreover, depending on the particle shape, the relationship exhibits diverse behaviors. For spherical-shaped particles, yield stress decreases rapidly compared to irregular-shaped particles. It is noteworthy that the results fit well to the regression line for irregular-shaped particles and deviate from linearity for spherical-shaped particles, indicating that for irregular-shaped particles, yield stress primarily depends on WFT. Finally, the concurrence of the regression lines suggests that there is a WFT value at which the influence of particle shape on flow and rheology becomes insignificant. The pattern of the relationship between flow and yield stress is shown in Figure 12. An inverse linear relationship between flow and the logarithm of yield stress is obtained, showing that both measures are affected similarly. Additionally, flow spread is more sensitive at high flowability, whereas yield stress is more sensitive at low flowability.

Figure 11

The relationship between yield stress vs WFT.

Figure 12

Relationship between flow and yield stress.