Development of a Self-Regulating Solar Shading Actuator Based on the Thermal Shape Memory Effect

Abstract

In the field of adaptive building technologies, this research introduces the development of a self-regulating solar shading actuator that utilizes the thermal shape memory effect. The study focuses on addressing the actuator’s performance under diverse environmental conditions. Thermal simulations were carried out during the development of the individual components of the actuator and for the prediction of specific switching temperatures. The investigation includes an analysis of the sunshade’s response to varying environmental conditions, emphasizing its effectiveness on clear summer days and identifying challenges during overcast periods. The critical coordination between the solar collector and the shape memory alloy (SMA) wire is examined, shedding light on the impact of SMA temperature dynamics on the actuation performance. Through the integration of simulation data and real-world measurements, the study validates the thermal model for the solar collector, establishing the robustness of the system’s operation. This research work contributes significantly to the development of intelligent actuators and outlines the importance of validation of SMA-based applications under real conditions.

1. Introduction

An effective strategy for reducing the cooling energy demand of buildings involves the implementation of external shading systems. However, many current technologies are intricate and necessitate centralized control. Retrofitting existing buildings with external shading systems typically requires substantial renovation measures. To address this challenge and facilitate straightforward retrofitting, the research project “smartskinreal” [1,2] has developed an innovative and automatic shading system. The key lies in harnessing the thermal shape memory effect (SME) [3], which enables the development of a self-regulating solar shading actuator [4]. This system is capable of operating automatically, eliminating the need for electricity, sensors, or electric motors. It uses a metal wire made of a tailor-made shape memory alloy (SMA), which is placed within a thermal solar collector that serves as a heat source and is driven by solar radiation. By utilizing the thermomechanical properties of the SMA wire, the system actuates the slats of the shading system. This allows for the automatic adjustment of the shading based on external factors, such as the position of the sun and the temperature.

In this article, we provide a detailed insight into the development and functionality of the self-regulating sunshade system. The system consists of various components: the sunshade construction, the actuator, the collector, and the SMA wire. Initially, these components are examined and dimensioned separately. The design of the components is tailored to a temperate climate in Central Europe; however, it is fundamentally transferable to other climate zones and requirements. Subsequently, these components are assembled into a 1:1 demonstrator and tested under real conditions. The system is designed for automatic adjustment based on solar radiation without the need for electrical energy. We highlight the advantages of such a system for building climate control and discuss its significance for future applications.

2. Concept of the Self-Regulating Solar Shading Actuator

2.1. Sunshade Construction

We utilized a standard sunshade construction system as the foundational structure, comprising large rotating aluminum louvers [5]. Figure 1a depicts a 3D model, and (Figure 1b) presents a sectional view of the structure with its various standard components. The design was well established and had been used for shading purposes, primarily for external facade shading, for many years. It was commonly installed in buildings and met various static requirements according to EN 13659 [6]. Typically, the system was divided into smaller segments that could be arranged to shade large areas. The system could be positioned vertically and horizontally. Alternatively, it could also be used for ceiling shading, such as in outdoor terraces. The mechanics were designed in such a way that a building-specific number of louvers were securely connected together via a linkage rod. The louver angle was thus adjusted using a linear motor mounted on the linkage rod. Shifting the linkage rod caused a synchronized movement of connected louvers. Standard control was managed using a central control unit collecting and analyzing data from a weather station. Using relays, the individual louver segments were electrically controlled. Local user controls provided the flexibility to regulate individual or groups of shading units as required or to transfer control to an automatic system.

This chosen system allowed louvers to rotate up to 90° for actuation, according to the intended application of the technology utilizing the thermal SME. Figure 1c illustrates the mechanical principle underlying this integration. To connect the sunshade construction to the actuator, a louver was extended with a shaft. This extension enabled system control through a 90° rotational movement using the designated mechanical principle.

2.2. Shape Memory Effect

The shape memory effect describes the capability of some materials, such as shape memory alloys, to recover their initial shape after being apparently plastically deformed. The process can be thermal- and/or stress-induced. From an engineering point of view, SMAs present high actuation energy density [3,7]. SMAs can exhibit two different crystal structures: austenite (A) or high-temperature structure phase and martensite (M) or low-temperature phase. The transformation from one phase to the other is known as martensitic transformation. Each martensitic structure presents distinct orientation directions known as variants. The arrangement of these martensitic variants is manifested in two forms: twinned martensite ($M_t$), when the growth of the variants is self-accommodated and detwinned, or reoriented martensite ($M_d$), where a specific variant becomes dominant in one specific direction.

Under a mechanical load detwinned martensite can be induced from the twinned martensitic state [8,9]. This process involves reorienting a certain number of variants in the favorable direction. Detwinning leads also to a noticeable change in the material’s shape, which is almost retained even after the load is removed. However, the applied load must reach a certain threshold to initiate the detwinning process, known as the detwinning start stress ${\sigma }_s$. If the load achieves a sufficiently high level, complete tdetwinning of the martensite occurs. This stress level is referred to as the detwinning finish stress ${\sigma }_f$. Figure 2a illustrates the various points and the material behavior schematically.

When the material is subjected to a mechanical load higher than ${\sigma }_s$ in the austenitic phase, the phase transformation during cooling leads directly to the formation of detwinned martensite, causing a change in shape. Upon heating the material under a constant load, shape recovery occurs, and thus it is a reversible process [3]. The phase transition from austenite to martensite is termed forward transformation and the transition back to austenite is called reverse transformation. The martensitic transformaton is characterized by four singular temperatures that are stress-dependent. On the one hand, the forward transformation is determined by $M_s$ and $M_f$ as the martensite start and finish temperatures, respectively. On the other hand, the reverse transformation is illustrated by $A_s$ and $A_f$ as the austente start and finish temperatures, respectively.

The pseudoelastic behavior of SMAs is associated with the stress-induced phase transformation. Above $A_f$, large reversible strains are feasible upon monotonic loading and unloading. A typical pseudoelastic thermomechanical loading path concerns a transformation between (stable) austenite and detwinned martensite. Figure 2b shows an example of a stress–strain diagram during the pseudoelastic transformation between austenite and martensite.

2.3. Actuator Concept

The developed actuator assembly consisted of several components: sunshade construction, drive, counterweight, SMA-wire, and solar collector (cf. Figure 3). The sunshade construction was modified, with the linear motor being removed. The axis of the top louver was connected to an approximately 30 mm thick shaft, which penetrated the two sheets of the outer aluminum support profile and extended approximately 10 to 20 cm. All louvers were still flexibly joined to the linkage rod, and by rotating the top shaft by 90°, the entire sunshade construction was closed. The linkage rod was eccentrically positioned and, due to its weight, ensured the opening of the sunshade construction when the louvers were horizontally arrangedin absence of external forces.

The designed drive consisted of a pulley that guided a flexible wire rope. On one side of the wire rope, the SMA-wire was attached, while the other side was weighted. The weight provided stability to the sunshade construction and prevented the misalignment of the louver angle due to wind or user interference. Furthermore, the weight ensured a constant mechanical tension in the SMA wire. This was particularly important for utilizing the detwinned martensite-to-austenite transformation, as it helped to maintain stable SMA characteristics. Otherwise, external forces such as wind loads on the louvers of the sunshade construction could shift the characteristic temperatures due to varying mechanical stresses in the SMA wire. We expected this approach to yield reproducible results in the switching behavior of the actuator. In this study, we have utilized the thermal-induced phase transformation between detwinned martensite and austenite.

The SMA-wire was enclosed within a thermal solar collector for the thermal activation [10]. Therewith, temperatures significantly higher than the outdoor ones could be achieved when the collector was directly exposed to solar radiation. Hence, the activation temperatures of the SMA wire could be purposefully achieved. The selected heat transfer medium inside the solar collector was air. The heating of air within the solar collector is based on the greenhouse effect. It is similar to the process of a room being heated in summer by solar radiation passing through glass surfaces. The collector was thus used as a temperature-controlling element triggered by solar radiation. The solar collector consisted of a transparent PMMA tube and a concentrically located black-painted aluminum tube. The two tubes were connected via a shaft seal at each end, which hermetically sealed the air gap between them. The aluminum tube contained the SMA wire and was hermetically sealed on both ends by special cover points. Figure 4 depicts the cover points in a 3D model of a solar collector. The upper cover point included an axially movable shaft for transmitting the displacement of the SMA wire to the actuator. The shaft was equipped with two shaft seals. At the lower connection point, the wire ends were permanently clamped using screws, and connections were provided for electrical contact.

The aim of the project was a solar shading actuator that was powered only by solar heating and without electrical energy. However, for the development phase, we had integrated electrical connectors for joule heating into the system [11,12,13]. This simplified testing of the actuator in terms of functionality, fatigue, or demonstration. It was important that the system could still operate primarily without electrical energy. To apply efficient electrical heating, we employed 4 SMA wires within the solar collector. The wires were mechanically attached in parallel and electrically connected in series. The implemented configuration increased the electrical resistance while maintaining the same mechanical performance compared to a single thicker wire. This allowed for the electrical heating to operate with Safety Extra Low Voltage (SELV) according to IEC 61140:2016 [14]. The long wire, as shown in Figure 4, was tensioned using three ceramic rollers with a diameter of $7.5$ mm.

In principle, the SMA wire did not move over the rollers but remained constantly tensioned over them in a fixed position. Frequent movement of the SMA wire over the rollers would lead to the bending of the wire. This would damage the wire in the long term and should be avoided to ensure the functionality of the system. Additionally, the constant loading on the bent sections of the SMA wire could cause long-term damage. Microcracks could form in the vicinity of the bending point due to the volume expansion associated with the martensitic transformation [15,16,17]. To prevent fracture failure of the SMA at these locations, a low mechanical load was required.

The SMA wire was attached to the lower cover point of the solar collector (cf. Figure 4). We used two screws, each with a hole drilled through the shaft, through which the wire ends were threaded. A nut was used to press the wire ends between two copper washers. This resulted in the SMA wire being severely weakened at these points. To prevent the SMA wires from breaking at these points, the tensile strength of the material was only utilized to a small extent when designing the actuator. The two screws were also the electrical connection and the lower cover point was printed from an ultraviolet-resistant plastic.

3. Actuator Component Design

3.1. Actuator Parameters

The design of the actuator components and the selection of the SMA-wire depended on several factors. To calculate the resulting force on the SMA wires, $F_{SMA}$, a balance of forces was applied considering the system in mechanical equilibrium (1). Relevant factors were the wire cross-section $A_{SMA}$, the number of parallel SMA wires, the system’s mechanical resistance, and the restoring force of the counterweight $F_{weight}$. While adjusting the mass of the counterweight was relatively straightforward, the system resistance was a dynamic factor that depended on the external conditions and the angular position. External conditions included wear or contamination of sliding bearing connections in the sunshade construction system, resulting in changes in friction coefficients. Additionally, physical effects, such as the thermal expansion of the shading system components and alterations in resistance forces $F_{res}$ under summer and winter conditions, caused an impact on the required SMA forces. Wind forces could exert an impact on the system. A detailed analysis of the external forces was not within the scope of this work, and estimations were considered based on simulated tests.

The mechanical equilibrium is considered as

$$F_{SMA}=F_{res}+F_{weight},$$

(1)

then:

$${\sigma }_{SMA}·A_{SMA}=M_{res}·r_{actuator}^{-1}+m_{weight}·g.$$

(2)

The resistance force $F_{res}$ can also be represented as a resistance torque $M_{res}$ by dividing it by the actuator radius $r_{actuator}$. The weight force must be greater than the resistance force so that the counterweight could open the sun shading construction system $F_{res}<F_{weight}$. A large actuation radius actuator $r_{actuator}$ led to a reduction in the SMA forces to overcome the resistance forces. For this aim, a pulley was integrated as a standard component. The actuator radius $r_{actuator}$ was calculated based on the dimensions of the pulley $r_{pulley}$ and the wire rope diameter $d_{rope}$ as follows:

$$r_{actuator}=r_{pulley}+d_{rope}·0.5.$$

(3)

From the required rotation angle to close the shading system given by 90°, the length of the SMA wire $l_{SMA}$ could be dimensioned.

$$l_{SMA}·{ϵ}_{SMA}=r_{actuator}·\pi ·0.5$$

(4)

The effective functional length of the SMA wire was limited by the system. The experimental setup of the actuator should not exceed the height of the shading system. With a maximum length of the collector of 2.35 m, the maximum length was limited to $l_{SMA}\le 2.00$ m. According to the Clausius–Clapeyron relation, an increase in the mechanical stress causes a rise in the transformation temperatures $A_s$, $A_f$, $M_s$, and $M_f$. The stress–temperature variation can be described by the Clausius–Clapeyron coefficient C [MPa K⁻¹], which is SMA-specific. To calculate the transformation temperatures of the SMA, the setpoint switching temperatures determined in Section 3.3.3 are used. Their calculation is performed using Equations (5) and (6).

$$A_s^{\sigma }=A_s-{\sigma }_{SMA}·C_A^{-1},$$

(5)

$$M_s^{\sigma }=M_s-{\sigma }_{SMA}·C_M^{-1}$$

(6)

where $C_A$ and $C_M$ are the Clausius–Clapeyron coefficients of the austenitic phase transformation and martensitic phase transformation. The selection of the appropriate SMA was based on the requirements and data from the literature [18,19,20]. Equations (1)–(6) were used to dimension the components of the actuator.

3.2. Definition of the Shading Requirement

The first step of the SMA actuator design was to define and develop the automatic control of the solar collector. The system should primarily be automatically driven by the intensity of solar radiation. Therefore, the components should be designed to activate and deactivate the shading according to specific requirements. Initially, the open–close criteria of the sunshade louvers should be determined. The purpose of a sunshade system is to control solar radiation and protect the building from direct sunlight. An effective sunshade system takes into account the specific requirements of the building, geographical conditions, and individual user preferences. It should provide a balanced combination of protection against overheating and utilization of natural daylight to ensure a pleasant indoor environment while maintaining high energy efficiency.

Typically, a sunshade system should be closed when the solar radiation is too intense and when there is a risk of overheating the interior room, especially during the summer months and periods of direct sunlight. The sunshade system should reopen when the solar radiation decreases. As reference values for possible criteria for sunshade operation, specifications from DIN 4108-2 [21] were used. According to these specifications and in the absence of specific control parameters, a radiation-dependent control can be assumed. For windows oriented north, northeast, and northwest, the irradiation limit value amounts to 200 W/m² for residential buildings or 150 W/m² for non-residential buildings. For all other orientations, an irradiation limit value of 300 W/m² for residential buildings or 200 W/m² for non-residential buildings is used. The irradiation limit ($I_{lim}$ [W/m²]) describes the solar radiation intensity as the sum of direct and diffuse radiation perpendicular to the window. The values specified in DIN 4108-2 for $I_{lim}$ define ranges in which the sunshade should be closed.

Instead of the irradition, there are sunshade controls that utilize the illuminance ($E_v$ [$lx$]) as a control parameter [22,23]. The main advantage of these control systems is the cost-effective sensors. However, it is generally accepted that the resulting global radiation on the window surface represents the relevant control parameter for sunshade systems. Consequently, the radiation was chosen as the relevant control variable. Numerous studies have already been conducted to define the irradiation limit as a control parameter [24,25,26].

The sunshade construction system of this work slightly shaded the facade even in the open state. Therefore, the typical irradiation limit values for closing the shading tend to be slightly higher than for systems that are completely open. The provided standard control system utilizes a simplified approach by measuring the illuminance in [$lx$] on a horizontal surface. By calculating the solar position based on location and time, the individual shading elements are activated or deactivated according to their orientation. Nevertheless, the conversion between illuminance and solar irradiation can not be performed accurately. Therefore, assumptions regarding the $I_{lim}$ as reference values were realized for the design of SMA-controlled solar shading actuator.

3.3. Determination of the Design Temperatures for the SMA Transformation

The temperature of the SMA wire influences the angular position of the sunshade construction. The correlation between the thermo-mechanical properties of the SMA wire, the mechanical wire tension, and the temperature in the solar collector defined the shading system’s switching operations. In order to open and close the system as per the requirements, thermal investigations have been conducted. In a thermal model, the temperatures of the SMA wire within the solar collector were calculated based on the outdoor air temperature and solar radiation. The model was validated with measurement data. By using the model, switching threshold temperatures at which the SMA-wire should close ($A_{f,set}$) and open ($M_{f,set}$) were defined. These calculation results were used to select the appropriate SMA.

3.3.1. Model Approach for the Thermal Description of the SMA-Wire

The employed model aimed to comprehensively describe the thermodynamic behavior of the developed system, known as a smartskinreal system, particularly the heat transfer process within the system. The influences of both conduction and thermal storage, as well as radiation, were regarded to enable a precise prediction of the system’s thermal behavior. The conduction within the system was considered through the thermal properties of the materials, specifically for the materials of the solar collector and the SMA wire. A material database was utilized to assign thermal conductivities and specific heat capacities to the model. Enclosed air layers were treated as equivalent. Furthermore, radiation was considered as another significant heat transfer mechanism in the model. When radiation strikes a body, a part of it is reflected, a part is absorbed, and if the material is transparent, a part is transmitted. The fraction of incident radiation that is reflected is defined as the reflection coefficient $\rho$, the absorbed fraction as the absorption coefficient $\alpha$, and the transmitted fraction as the transmission coefficient $\tau$. According to the first law of thermodynamics, the sum of these three components must be one. Opaque bodies do not transmit radiation, and $\tau =0$ [27]. Figure 5a illustrates the basic solar model. A large part of the incident solar radiation energy is transmitted through the outer tube made of translucent PMMA. A significant part of this radiation is then absorbed by the absorber surface of the inner black-painted aluminum tube. This heat warms the enclosed air chamber within the inner tube. The SMA wire is located inside the air chamber. To model the wire temperature in the collector, we utilized the hygrothermal simulation software Delphin 5.9 [28]. The collector construction was simplified and transferred in a horizontal 1D roto-symmetric transport construction model. We assumed that the temperature inside the aluminum tube was largely uniformly distributed. Therefore, we could place the SMA wire in the center of the tube in the model as a metallic wire with a diameter of 1 mm. This specific diameter was chosen due to the limitations of the software. Adjacent to it, a stationary air layer was assumed with the corresponding radius of the aluminum tube, as well as an aluminum layer with the wall thickness of the inner tube (see the model in Figure 5b). Due to software-specific limitations for defining radiation transmission, the boundary conditions were directly applied to the inner black-coated aluminum tube. However, to account for the outer transparent acrylic glass tube, modifications were made to the heat transfer resistances and absorption coefficient. For the consideration of enclosing PMMA pipes, the external static transition resistance $R_{se}$ was adjusted. The modified temperature transition resistance to the outside air $R_{se}^{\ast }$ resulted in

$$R_{se,mod}=R_{se}+R_{Air}+R_{PMMA}.$$

(7)

The temperature transition resistance was thus increased by the temperature transmission resistances of the stationary air layer $R_{Air}$ and the PMMA tube $R_{PMMA}$. The modified emissivity of the surface of the aluminum tube ${\alpha }_{Alu,mod}$ was obtained through multiplication with the total energy transmittance of the transparent acrylic glass tube ${\tau }_{PMMA}$. Due to the symmetry conditions of the 1D roto-symmetric model, the incident direct and diffuse radiation fractions were each halved. This was because the incident direct radiation hits the absorber surface of the tube with only half of the surface:

$${\alpha }_{Alu,mod}={\tau }_{PMMA}·{\alpha }_{Alu}·0,5.$$

(8)

By implementing the model, temperatures of the SMA wire in the collector could be calculated as a function of the outdoor climate. With the thermo-mechanical properties of the SMA-wire, predictions about the switching behavior could be conducted.

3.3.2. Experimental Validation of the Model

The model validation was realized through the comparison of simulated results with experimental data from real-world trials. Various scenarios and boundary conditions were considered over a continuous period of 14 days to ensure an accurate model. The experimental setup included the developed collector with a length of 1 m. It was located on the roof of a three-story building in Leipzig, Germany, oriented to the south and not shaded by surrounding structures. The top and bottom openings were sealed against air and water. A temperature sensor was installed in the center of the inner air chamber of the collector. We assumed that the air temperature in the center of the solar collector corresponded to the temperature of the SMA wire. This assumption was based on the fact that the sensor and sensor wiring were made of a metallic wire similar to the SMA-wire, and their properties were expected to be comparable. Furthermore, the recording of boundary conditions includes outdoor air temperature and south-facing solar radiation. With a measurement output at 10-min intervals, data from April to May 2020 over a period of 14 days were available. The measured boundary conditions were also implemented as boundary conditions in the model. For the simulation period, the temperatures of the SMA wire in the center of the collector were calculated and compared with the available measurement data. The measured and simulated data showed a high degree of agreement. The simulations were run with hourly mean values. In contrast, the measurement data were entered as 10-min mean values. This could be one reason why the simulated data showed a more stable curve. Figure 6 illustrates an exemplary comparison plot.

3.3.3. Defining SMA Setpoint Switching Temperatures

In the next step, we used the validated model to define the SMA setpoint switching temperatures. They describe the theoretical SMA temperatures at which the sunshade construction should start to close (${\vartheta }_{A,set}$) and open (${\vartheta }_{M,set}$). The martensitic transformation from austenite to martensite and vice versa does not occur at a specific temperature but within a temperature range. It was evident that this behavior also influences the switching dynamics of the sunshade construction. Therefore, the sunshade construction could not abruptly close upon reaching a specific temperature. The SMA setpoint switching temperatures should broadly define the martensitic transformation between $A_s^{\sigma }$ and $A_f^{\sigma }$ or $M_s^{\sigma }$ and $M_f^{\sigma }$. These temperatures of the SMA-wire were reached when the solar irradiation of the facade surface overtook the limit values determined in Section 3.2,

Table 1. Defined irradiation limit values as variables for the control of the sunshade construction system.

Parameter	Symbol	Value	Unit
Solar irradiation during the time when the sunshade should close	$I_{lim,close}$	400	W/m2
Solar irradiation during the time when the sunshade should open	$I_{lim,open}$	150	W/m2

. For this purpose, SMA temperatures ${\vartheta }_{SMA}$ and irradiation of the vertical surface $I_{vertical}$ were calculated with the model for different orientations. We used a climate dataset TRY-4 Potsdam, Germany [29], as boundary conditions. The dataset included outdoor air temperature and radiation data, which were used for the validation of the data. Figure 7 shows the simulation results on this topic using a single day in summer as an example. The irradiation limit values $I_{lim}$ to open and close the system are shown as a step curve. The model calculated the ${\vartheta }_{SMA}$ based on the TRY-4 radiation data. Subsequently, the corresponding ${\vartheta }_{SMA}$, at which the sunshade construction system should open and close, was determined using $I_{lim}$. These temperatures corresponded to the stages when $I_{vertical}$ reached the respective $I_{lim}$ values. The ${\vartheta }_{SMA}$ for opening and closing were provided for these time points. The smartskinreal sunshade construction system was designed to generally react accordingly to temperature variations with a desired gradual and uniform opening and closing of the louvers. The simulation data revealed that the differences between the ${\vartheta }_{SMA}$ for opening and closing were sometimes very narrow. This was problematic for the selection of a fitting SMA wire. We therefore collected the ${\vartheta }_{SMA,20}$ from the simulation results. This dataset described the SMA temperatures obtained 20 min after the solar irradiation reached the limit value $I_{lim}$. We assumed that a delay of 20 min for the opening and closing of the louvers was an acceptable compromise.

Figure 8 presents the results of the simulations for ${\vartheta }_{SMA,sim}$ for one summer period from April 1 to September 30. The data distinguish between two variants: Figure 8a,b. In variant Figure 8a, temperatures of the SMA wire are provided at the time when solar irradiation I reach the threshold values $I_{lim}$. In variant Figure 8b, temperatures were calculated 20 min after reaching the threshold values. We developed the second variant for a better estimation of the dynamics of temperature trends in the solar collector. Both variants differentiated between the events for closing ${\vartheta }_A$ (shown on the left in red) and opening ${\vartheta }_M$ (shown on the right in blue) of the louvers. The data exhibited a significant scattering of values. This was due to the fact that during cloudy periods, irradiation values on the facade surface could rise and fall abruptly. In contrast, the data in Figure 7 represent a mostly cloudless day, where solar irradiation I varies smoothly over the course of the day. The high scattering was thus attributed to the inertia of the solar collector during heating and cooling. Furthermore, it could be possible that on a cloudy day, $I_{lim}$ could only be briefly exceeded or undershot. The sluggish behavior could help to avoid the rapid opening and closing of the louvers. Consequently, the differences in medians between ${\vartheta }_A$ and ${\vartheta }_M$ increased from $\Delta \vartheta =3.0$ K in variant Figure 8a to $\Delta \vartheta =14.6$ K in variant Figure 8b. The simulation data covered a whole summer period. Particularly low temperatures in the solar collector along with high irradiation values could be attributed to cold outdoor air temperatures. This granted the utilization of solar gains during cold seasons. Despite the high variability in the simulation results, the heating of the solar collector could be compared to the solar heating of indoor spaces. The goal of the sunshade construction system was to avoid overheating in rooms during summer. This implies that the dynamics of solar heating in the solar collector may behave similarly to the heating patterns of the protected rooms.

In order for the sunshade construction to open fully again at low irradiation, the SMA temperature had to decrease. In some cases, the solar collector heated the SMA wire well above the temperature of the ambient air. During the martensitic transformation from austenite to martensite, the temperature could only drop to the ambient air temperature. This means that the ambient air temperature significantly influenced the opening behavior. If the ambient air temperature remains consistently above $M_f^{\sigma }$ throughout the night, the sunshade construction will not fully open during the night. This would clearly indicate a system malfunction. In the temperate Central European climate, tropical nights occur only occasionally. Tropical nights are weather events with air temperatures above 20 °C during the night. Therefore, an additional SMA setpoint is recommended that is defined as $M_f^{\sigma }>20.0$ °C.

Based on the general considerations and the calculation results from the simulations, SMA setpoint switching temperatures are defined; see

Table 2. Defined SMA setpoint switching temperatures for the selection of the SMA.

Parameter	Symbol	Value	Unit
Sunshade during the closing process	${\vartheta }_{A,set}$	45.7	°C
Sunshade during the opening process	${\vartheta }_{M,set}$	31.1	°C
Sunshade opening process is complete	$M_f^{\sigma }$	>20.0	°C

.

3.4. Determination of the System Resistance

The resistance force $F_{res}$ of the sunshade construction system was an essential input parameter for the drive design. It describes the force required to move the louvers. Thus, it was the force that the actuator must apply to open and close the system. Since the force transmission of the actuator to the sunshade construction system took place through a ${90}^{°}$ rotary motion, the resistance force $F_{res}$ was described by a resistance torque $M_{res}$ (Equation (9)). $M_{res}$ comprised different components: firstly, the friction of the plain bearings, in which the lamellas are supported; secondly, the weight force of the eccentrically arranged push rod, which contributed to $M_{res}$; and finally, the environmental effects due to wind, snow, and rain, which also influenced $M_{res}$. It must be emphasized that the components are particularly variable. For instance, the friction in the sliding bearings of the louvers is time- and assembling-dependent. Therefore, $M_{res}$ could only be approximated.

For a realistic estimation of $M_{res}$, we performed measurements on an existing sunshade construction system like the smartskinreal system. As already stated for the actuator concept, the measurements were performed using the ${90}^{\circ }$ rotary motion of a drive shaft. A pulley with a rope mounted on the drive shaft and attached to a load cell was employed for the measurements. In a stationary mechanical state, the sunshade is open due to the weight of the push rod. Thus, the sunshade system could be closed by pulling on the rope with the load cell. For good reproducibility, several trials were carried out by manually pulling the rope to determine the $M_{res}$ of the sunshade system. Finally, the forces determined by the load cell were multiplied by the radius of the pulley to obtain $M_{res}$ (Equation (9)).

$$M_{res}=F_{res}·r_{actuator}.$$

(9)

In Figure 9, the experimental setup Figure 9a and the results Figure 9b of the measurements are depicted. The results for $M_{res}$ are shown over the duration time of the experiment. The data trend presented a continuous increase in $M_{res}$. Between approximately 3 and 6 s, the breaking torque was developed. It was reached at about 3 Nm. Between seconds 6 and 15, the sunshade construction system was closed. During this period, $M_{res}$ increased by about 1 Nm. The latter increase can be attributed to the required force to raise the connecting push rod that links all the louvers. In the closed state, $M_{res}$ attained a maximum of approximately $4.5$ Nm. The measurement data for $M_{res}$ provided reference values for the actuator design. Additional factors such as wind or snow were not taken into consideration.

3.5. Selection of the Shape Memory Alloy

Based on the results of the preceding subsections, the selection of a suitable and commercially available SMA was accomplished. NiTi alloys are the most widely used SMAs, finding extensive applications due to their excellent mechanical properties, corrosion resistance, and characteristics, such as both the shape memory effect (SME) and superelastic SMAs [3,30]. Substituting portions of nickel with copper in the alloy composition reduces both the thermal hysteresis and the transformation stress of NiTi alloys. Although any modification in the composition of a binary NiTi alloy strongly influences the transformation temperatures, the addition of copper to binary NiTi alloys significantly diminishes the sensitivity to transformation temperatures [30,31]. The optimal composition range is found between 5 at-% Cu and 10 at-% Cu in the Ni-Ti-Cu alloys [3]. Furthermore, the addition of chromium increases the yield stress, contributing to the overall strengthening of the alloy [32]. The influence of mechanical stress on the selection of a suitable SMA alloy is of great importance. As stress increases, the transformation temperatures between states also change according to the Clausius–Clapeyron relation. The relationship can be described using the Clausius–Clapeyron coefficient C [MPa K⁻¹]. For NiTi alloys, a wide range of values, from 4 to 20 MPa K⁻¹, are reported in the literature [33]. In Section 3.1, Section 3.2, Section 3.3, Section 3.4, the fundamentals for the actuator design have been presented. These were applied to develop the self-regulating solar shading actuator. Equations (1)–(6) were computed to determine the actuator’s parameters and select a suitable SMA. The meaningful factor for the SMA selection was the requirement from Section 3.3.3 above $M_f^{\sigma }>20.0$ °C, so that the sunshade construction opens reliably even on tropical nights. For the intended application, a $N{i}_{42.5}T{i}_{49.8}C{u}_{7.5}C{r}_{0.2}$ SMA-wire with a diameter of $d_{SMA}=0.76$ mm was chosen.

Another important aspect was determining the exact strain of the SMA wire (${ϵ}_{SMA}$). This value was heavily dependent on the existing SMA tension (${\sigma }_{SMA}$) (cf. Section 2.2). We assumed that due to imperfections in the actuator’s manufacturing, the wire tension could slightly deviate from calculated values. To counter this issue, we estimated the SMA strain at 4% and built the system without the solar collector. We used the electrical connections to heat the SMA wire, thereby changing the angle of the louvers. Through the measurement data from the rotation of the louvers in this experiment, we were able to calculate the exact value of ${ϵ}_{SMA}$ for the full-scale demonstrator (cf. Section 4). Should there be a change in the construction setup, ${ϵ}_{SMA}$ would likely change as well. The design parameters are presented in

Table 3. Design parameters for the control of the sunshade construction system.

Parameter	Symbol	Value	Unit
Length of the SMA-wire	$l_{SMA}$	1.92	m
Actuator radius	$r_{actuator}$	0.0343	m
SMA cross-sectional	$A_{SMA}$	1.81	mm2
Weight force	$F_{weight}$	147.0	N
Resistance torque	$M_{res}$	4.5	Nm
Resistance force	$F_{res}$	131.0	N
SMA tension	${\sigma }_{SMA}$	71.4	N mm−2
SMA strain	${ϵ}_{SMA}$	2.9	%
SMA stress influence coefficient	C	4.425	MPa K−1
Martensite start temperature	$M_s$	28.2	°C
Martensite finish temperature	$M_f$	4.9	°C
Austenite start temperature	$A_s$	26.3	°C
Austenite finish temperature	$A_f$	43.6	°C
Martensite start temperature under tensile stress ${\sigma }_{SMA}$	$M_s^{\sigma }$	44.3	°C
Martensite finish temperature under tensile stress ${\sigma }_{SMA}$	$M_f^{\sigma }$	21.0	°C
Austenite start temperature under tensile stress ${\sigma }_{SMA}$	$A_s^{\sigma }$	42.4	°C
Austenite finish temperature under tensile stress ${\sigma }_{SMA}$	$A_f^{\sigma }$	59.7	°C

.

4. Validation of the Full-Scale Demonstrator

Considering the findings outlined in Section 3, a full-scale demonstrator was constructed with the primary objective of assessing the functionality. This entails the validation of theoretical models, assumptions, and outcomes in real-world conditions. The demonstrator was attached to a climate test cell, providing the capability to shade a fixed glazed section of a mullion-transom facade system. The internal climate within the test cell was subjected to monitoring and control, enabling an analysis of the sunshade’s impact on indoor environmental conditions. The demonstrator is located in Leipzig, Germany, on the campus of the University of Applied Sciences. Situated in a westward orientation, the shaded facade area was supported by a static structure designed for the seamless connection of diverse components and efficient low-friction force transmission. To facilitate a comprehensive assessment, an array of sensors were strategically incorporated for monitoring purposes. Subsequent to data collection, an analysis was conducted, drawing comparisons between the observed data and the theoretical models developed. A time-lapse video of how the full-scale demonstrator works on various summer days was attached to this article at Supplementary Materials.

4.1. The Demonstrator Setup

The implementation of the full-scale demonstrator required a static structure that seamlessly provided the assembly of the components. Consequently, we designed a prototype where the actuator components were positioned externally to the conventional components of the sunshade construction system. This strategic arrangement conferred the advantages of simplified component replacement and increased adaptability for the integration and substitution of sensors. The components constituting the sunshade construction system were predominantly preserved in their original configuration.

For the sunshade construction, a total of 13 aluminum louvers, each with a depth of 20 cm and a width of 195 cm, were systematically arranged. This arrangement resulted in a shaded area of 270 cm in height and 195 cm in width. The louvers were securely affixed on both the left and right sides within aluminum rectangular profiles through sliding bearings. A linkage rod joined all the louvers. The coupling to the actuator was established through a shaft positioned within the topmost louver. The shaft traversed the left rectangular profile and was supported by sliding bearings. On the left side of the sunshade construction, two angle profiles (top and bottom) made from 10 mm thick stainless steel sheets were securely mounted. These profiles provided stable support for the actuator components. At the upper profile, the shaft was additionally supported by two bearing blocks. The shaft was mounted with minimal friction through double ball bearings. A pulley, as the actuator drive, was securely fixed to the shaft. Enclosed within the pulley was a wire rope that linked the counterweight on one side and the solar collector with the SMA wire on the other side. To ensure stability and mitigate the rattling of louvers during windy conditions, a spring-loaded cam disc was coupled to the shaft. This disc was designed to maintain the louver positions at 0°, 45° and 90°. Integrated sensors enabled the monitoring. A solar irradiation sensor, positioned at a 90°, precisely measured the solar irradiation on the facade surface. It also was capable of simultaneously recording the ambient air’s temperature and relative humidity. Additionally, measurements of the louver angle and the temperature at the center of the solar collector were systematically acquired. The installed monitoring system collected data diligently over an extensive period of time, specifically from 1 June to 31 August 2023. Data retrieval from the sensors was facilitated by a data logger operating at a rate of three values per second. Figure 10 visually represents the components of the full-scale demonstrator.

4.2. Sunshade Function

The shading function of the system was first ascertained. The operating points for the opening and closing operations were determined. In Section 3.2, the irradiation on the facade was defined as the primary requirement for louver activation. Figure 11 presents irradiation data for three exemplary days. In the year 2023, 6 July was a lightly cloudy summer day, August 6 was more overcast, and August 11 was a cloudless summer day. The measured irradiation data and the threshold values from Table 1 were utilized to calculate the ideal louver angles. These data are also depicted in Figure 11 and are superimposed to the measured louver angles. Calculations and measurements exhibited a high correlation on the cloudless summer day. On cloudy days, the louvers either did not close, or a partial and delayed closure was monitored. The louver closing started partly before and after reaching the irradiation threshold of $I_{lim,close}=400$ W m⁻². The louver opening began as estimated, ending shortly below the irradiation threshold of $I_{lim,open}=150$ W m⁻². In general, the switching process (closing and opening) proved to be markedly sluggish, extending over an hour in some instances. On 11 August 2023, a deviation in the louver angle of approximately 88° was recorded, which closely corresponds to the intended rotation of 90°.

Principally, the functionality of the system was validated. Particularly on clear summer days, the system fulfilled the specifications and requirements. On overcast days, the system either partially closed or did not close at all. These outcomes seemed reasonable, as the primary purpose for shading was not as demanded or given under such sky conditions. The issue arose when the louvers either closed with a significant time delay or, in some cases, did not close at all during partially cloudy conditions or sudden high irradiation on the facade. This delay was likely attributed to a certain inertia in the heating of the solar collector.

4.3. Solar Collector

An essential issue of the system was the coordination between the solar collector and the SMA wire. The SMA wire was located in the inner air chamber of the solar collector. Solar radiation hit the solar collector, and the inner air chamber heated up. As solar radiation on the collector decreased due to transmission heat losses to the surroundings and minor air leaked in the solar collector, the inner air chamber’s temperature dropped. In the monitoring process, we measured the temperature in the inner air chamber, assuming that the temperature of the SMA-wire was almost similar. Data from Section 4.2 indicated that the closing process of the louvers could be time-consuming. This suggests that the heating of the SMA wire within the inner air chamber of the solar collector occurred slowly. In Figure 12, we compare the measured SMA temperatures with the material characteristics of the selected SMA. To illustrate the heating of the solar collector, we utilize the three exemplary summer days from Section 4.2 and Figure 11 (6 July 2023, 6 August 2023, and 11 August 2023). In Figure 12, we present the outdoor temperature alongside the SMA temperature inside the solar collector. Also depicted are the martensitic transformation temperatures of the integrated SMA-wire at the ideal time of each switching event ($M_s^{\sigma }$, $M_f^{\sigma }$, $A_s^{\sigma }$, and $A_f^{\sigma }$). For a reliable operation of the sunshade construction, the SMA temperature should follow a steep rise and fall within the range between the start and the finish temperatures. During the martensitic transformation, the SMA temperature on all three exemplary days correlated with the desired switching time within the setpoint temperatures $M_s^{\sigma }$ and $M_f^{\sigma }$. Consequently, the switching process for opening the sunshade construction was fulfilled. The austenitic transformation only corresponded with the desired switching time within the setpoint temperatures $A_s^{\sigma }$ and $A_f^{\sigma }$ on 11 August 2023. For 6 July and 6 August 2023, the SMA temperature at the appropriate switching time was below $A_s^{\sigma }$. The closing process of the sunshade construction was significantly delayed on 6 July 2023, and on 6 August 2023, the louvers were only rotated by a few degrees. The developed system accomplished the criteria with limitations. To ensure a stable opening function of the system on particularly hot nights, $M_f^{\sigma }=21.0$ °C was chosen. As a consequence, the austenite transformation temperatures, $A_s^{\sigma }=42.4$ °C and $A_f^{\sigma }=59.7$ °C, were slightly raised, leading to a delay in closing the sunshade construction under less intense solar irradiation.

The setpoint switching temperatures, as detailed in Section 3.3.3, were established to achieve specific temperatures at particular irradiation levels. These temperature thresholds (refer to Table 2) corresponded to the conditions prevailing within the solar collector when the facade’s irradiation surpassed predefined thresholds (refer to Table 1). In Section 3.3, a thermal model for the solar collector was developed and validated. The theoretical model was applied to the measurement data from the full-scale demonstrator. In the simulation, climate data were utilized as boundary conditions for defining the SMA setpoint switching temperatures. The aim was to ascertain whether comparable results for the SMA setpoint switching temperatures were obtained under real-world conditions. In Figure 13, we presented a comparative analysis, contrasting previously calculated data with measurements acquired from the full-scale demonstrator. The data underscored an agreement between simulated and real-world measurements. In particular, the measured data akin to our simulations exhibited a noteworthy range of variability. The model of the solar collector was therewith validated for the full-scale demonstrator too.

4.4. Analysis of SMA Characteristics

The material properties of the selected SMA should be identified in the collected monitoring data. Throughout the actuator’s operation, the SMA wire was consistently subjected to a constant mechanical stress of ${\sigma }_{\mathrm{SMA}}=71.4$ MPa. As a result, the SMA transformation temperatures underwent alterations influenced by the Clausius–Clapeyron coefficient C. This coefficient slightly varies for each transformation temperature; however, we used an average value $C=0.226$ K MPa⁻¹ to evaluate the properties. We compare temperature data in the inner chamber of the solar collector with the louver’s angular positions. The SMA temperature could not be measured accurately with the full-scale demonstrator setup. We assumed that temperature changes in the solar collector were gradual and the temperature differences between the SMA wire and the air inside the solar collector were negligible. In addition, the temperature sensor used in the solar collector consisted of two thin metallic wires with an NTC probe. These wires ran parallel to the SMA wire and entailed similar thermal properties. Therefore, we equate the temperature in the solar collector with the SMA temperature. Figure 14 illustrates SMA temperatures across louver angular positions. We deployed data from a representative period spanning from 1 June to 24 August 2023. Also shown are the martensitic transformation temperatures when the SMA wire is subjected to tensile stress ($M_s^{\sigma }$, $M_f^{\sigma }$, $A_s^{\sigma }$, and $A_f^{\sigma }$). They are plotted at the corresponding louver angles of 0° or 90°. In Figure 14, 5-min averages are presented as a curve set over many days. The resolution of the monitoring was too low to depict the relationship between SMA temperature and louver angle at each acquired point. The switching process should occur significantly faster than can be recovered with a 5-min measurement interval. However, the measurement and setup errors could also lead to inaccuracies in the diagrams, for example, the assumption of the same temperatures in the collector and on the SMA wires. In particular, the trends in the angular ranges between approx. 10° and 40° seemed to scatter. In regions below 10°, there is a partial spread. These corresponded to data from days in which the solar irradiation was not sufficient to close the louvers completely (cf. 6 August 2023, in Figure 11 and Figure 12). Similarly, data were distributed as point clouds in the angle range from approx. 50° to 80°, where the louvers were only partially closed (cf. 6 July 2023, in Figure 11 and Figure 12). Taking these points into account, a recurring pattern could be discerned from the data. The course from $M_s^{\sigma }$ to $M_f^{\sigma }$ described the forward martensitic transformation, and that from $A_s^{\sigma }$ to $A_f^{\sigma }$ described the reverse martensitic transformation. The theoretically computed transformation temperatures (in orange in Figure 14) could be validated, but for a few measurements, the were located slightly higher than acquired measurement data.

5. Conclusions

In conclusion, the development of a self-regulating solar shading actuator by means of the thermal shape memory effect set a further milestone in applications driven by SMA. The actuator’s primary function as a sunshade has been demonstrated and validated. In particular, the requirements were fulfilled on clear summer days.

However, future work should optimize the shading operation under varying sky conditions or on overcast days to avoid partial closure delays or even non-closure. This phenomenon was attributed to the thermal inertia in the solar collector, which im**ed on the dynamic performance response of the SMA wire.

The monitoring of SMA temperatures revealed how long a gradual closing process of louvers could last, indicating a sluggish heating of the SMA wire. While the system generally fulfilled the criteria, adjustments in SMA setpoint switching temperatures could enhance its dynamic response, especially in conditions of sudden high irradiation or partially cloudy situations. Lowering the SMA transformation temperatures, for example, by lowering the tensile stress in the SMA wire or changing the alloy composition, could improve the closing process but impair the opening process, particularly on warm nights. Another potential solution to this issue could be to increase the efficiency of the solar collector.

The validation of simulation data with real-world measurements verified the thermal model for the developed solar collector. The system’s performance in the full-scale demonstrator validated its functionality despite inherent variability in real-world conditions.

Despite challenges in directly measuring SMA temperatures, the study outlines the correlation between the temperature data in the solar collector and louver positions. The observed patterns align well with theoretical results, validating the function of the SMA in driving the sunshade construction.

Lastly, the developed system showcases commendable performance under optimal conditions. Further investigations of the solar collector and SMA wire, as well as adjustments in setpoint temperatures, can enhance the reliability and operational response across a broader range of environmental scenarios. The findings gained from this study will contribute valuable knowledge to the field of adaptive building systems, emphasizing the importance of real-world validation for smart and responsive technical solutions. The outcomes and results gathered with the developed components under real boundary conditions can be used in future works to develop new actuator systems.