Numerical Analysis of Experimental Research in a Lightweight Floor System (LFS) with Heat Diffuser

The article presents the results of research on a lightweight floor system (LFS) with a heat diffuser made of metal lamellae. It differs from traditional layered floors in the absence of a screed layer, which reduces thermal inertia and predisposes it to be used with renewable energy sources. As part of the research, a real model of the floor, consisting of nine ceramic tiles, was made. Polyurethane adhesive was used to connect the individual layers of this composite. The model was subjected to a thermal action. It was constructed with the measuring equipment consisting of strain gauges. These were located at the boundaries of the composite layers and measured the material’s deformation. The measurement results were verified by numerical calculations. For this purpose, a computational model was made using FEM (finite element method). Comparable results of deformations were obtained (the differences did not exceed 6.1%), which made it possible to perform numerical calculations of light floor materials stresses. Additionally, the displacement of the tested model was measured and numerically verified. The results of these verifications can be useful not only in the heated/cooled LFS with aluminium lamellae, but also in other building partitions inside and outside the building.


Introduction
In the modern world, there is an urgent need to search for technical material solutions conducive to the use of energy from renewable sources, as well as technologies that reduce its consumption. This topic is taken up by scientists and such problems can be found, for example, in [1][2][3][4]. Hence the need to use more efficient heaters. One solution could be floor or wall-mounted radiators. Heaters of this type have a layered structure with a built-in heating element-most often in the form of a heating coil or electro-resistance structures. Renewable energy sources are dependent on the weather. Therefore, it is justified to use heaters that use even small energy resources. Lightweight floor systems (LFS) are such a solution. These systems eliminate the energy accumulator, which is the heavy concrete slabs (screed). The floor layer (ceramic tiles) with an insulating layer was combined with the use of polyurethane adhesives, which spread easily and make the structure more flexible when exposed to changing temperatures. The use of this type of adhesive is also justified due to the good properties of mechanical compatibility. It is characterized as the product of the thermal expansion coefficient α multiplied by Young's modulus of elasticity E. Polyurethanes have a low TN value due to low E-values, despite high α values. Therefore, the thermal stresses arising in them do not cause the destruction of less-resistant substrates, and besides, they are able to withstand much greater deformations than materials with significant stiffness. The proper connection of layers with different mechanical parameters was dealt with in [5][6][7]. The topic of stress reduction using the dependence of dynamic and static modules, when there are temperature and pressure changes, and when obtaining an elastoplastic solution of stresses and strains while also dealing with the influence of heterogeneity in mechanical parameters, can be found in articles [8,9]. The above-mentioned works contributed to the introduction of polyurethane adhesives into the research. Thermal efficiency is to be increased by the used aluminium diffuser, the so-called lamellae. Aluminium was chosen because of its high thermal conductivity parameters and good cooperation in the well-matched polyurethane adhesives. The presented technical solution was subjected to experimental tests to determine the value of internal forces-stresses, in conditions similar to operational ones. As part of the research, a floor fragment, with dimensions of 3 × 3 ceramic tiles, was made. The model was subjected to a thermal action corresponding to the assumed average operating temperatures. The floor model was made together with the measuring equipment composed of strain gauges. The strain gauges were placed inside the composite at the boundaries of individual layers. Additionally, the digital image correlation (DIC) system was used to measure the model displacements. The results were checked by making a calculation model using FEM. Comparable results of deformations were obtained, which made it possible to perform numerical calculations of stresses inside the lightweight floor. The material parameters adopted in the computational analysis are summarized in Table 1. They are taken from the research included in [10][11][12][13][14][15][16][17][18][19][20][21][22]. Strength data and material parameters of the polyurethane adhesives used, such as Young's modulus E, Poisson number ν, and thermal expansion coefficient α, were obtained from the tests performed by Karpiesiuk [23,24]. The obtained results will be summarized and compared, which will allow for an assessment of the test's correctness.

Materials and Experimental Methods
In order to carry out a numerical analysis of the LFS tests with aluminium lamellae, immediately after determining the material parameters of individual layers of this lightweight floor type, it was decided to experimentally check the size of deformations and displacements caused by temperature. For this purpose, a model of a light heated floor with a heating coil and a heat-dissipating layer-lamellae-was prepared. The research was conducted at the Bialystok University of Technology with the use of strain gauge and digital image correlation (DIC) techniques. The set of DIG system devices is used for non-contact, three-dimensional measurements of deformations caused by static and dynamic loads. It is based on a series of photos taken with digital cameras to recognize the surface structure of the measured object (each pixel in the photo is assigned appropriate coordinates). The purpose of this method is to analyse, calculate displacements and document the deformation of the measuring material. Graphical presentation of the research results obtained enables a complete understanding of the behaviour of the tested object. The measuring stand was 60 × 60 cm, and the floor was covered with 20 × 20 cm tiles. Active strain gauges were placed at different levels of the system layers, between the central tile plate and the XPS. Before embedding, the strain gauges were attached to previously prepared substrates of the materials used in the test. Figure 1 shows the place of the strain gauges installation on the polyurethane adhesive. The experimental model of the lightweight floor consisted of 40 mm XPS thermal insulation with grooves where a 16 mm diameter heating coil was placed. The heating pipes were not fed with water, but with an Elektra UltraTec heating cable with unit power of 10 W/m. An aluminium lamella with a thickness of 0.06 mm with a 1 mm layer of Sika Force-7710 L100 polyurethane adhesive was used. The aluminium lamella was covered with 8.5 mm thick Tero ceramic tiles by Paradyz, fixed with Sika BondT8 polyurethane adhesive. The joints between the ceramic tiles were filled with C2S1 flexible cement mortar. The experimental model, with a similarly constructed smaller composite with dimensions of 20 × 20 cm, (necessary for the placement of passive strain gauges) is shown in Figure 2. Registration of the deformations and the temperature in the centre of the composite were determined according to the description in the article [25]. Additionally, in the same way, as described in [25], the deformations of seven active and passive strain gauges, installed on each of the LFS layers, were recorded.
The places of installation of the active strain gauges and temperature sensors in the central part of the model are shown in  The experimental model of the lightweight floor consisted of 40 mm XPS thermal insulation with grooves where a 16 mm diameter heating coil was placed. The heating pipes were not fed with water, but with an Elektra UltraTec heating cable with unit power of 10 W/m. An aluminium lamella with a thickness of 0.06 mm with a 1 mm layer of Sika Force-7710 L100 polyurethane adhesive was used. The aluminium lamella was covered with 8.5 mm thick Tero ceramic tiles by Paradyz, fixed with Sika BondT8 polyurethane adhesive. The joints between the ceramic tiles were filled with C2S1 flexible cement mortar. The experimental model, with a similarly constructed smaller composite with dimensions of 20 × 20 cm, (necessary for the placement of passive strain gauges) is shown in Figure 2. The experimental model of the lightweight floor consisted of 40 mm XPS thermal insulation with grooves where a 16 mm diameter heating coil was placed. The heating pipes were not fed with water, but with an Elektra UltraTec heating cable with unit power of 10 W/m. An aluminium lamella with a thickness of 0.06 mm with a 1 mm layer of Sika Force-7710 L100 polyurethane adhesive was used. The aluminium lamella was covered with 8.5 mm thick Tero ceramic tiles by Paradyz, fixed with Sika BondT8 polyurethane adhesive. The joints between the ceramic tiles were filled with C2S1 flexible cement mortar. The experimental model, with a similarly constructed smaller composite with dimensions of 20 × 20 cm, (necessary for the placement of passive strain gauges) is shown in Figure 2. Registration of the deformations and the temperature in the centre of the composite were determined according to the description in the article [25]. Additionally, in the same way, as described in [25], the deformations of seven active and passive strain gauges, installed on each of the LFS layers, were recorded.
The places of installation of the active strain gauges and temperature sensors in the central part of the model are shown in  Registration of the deformations and the temperature in the centre of the composite were determined according to the description in the article [25]. Additionally, in the same way, as described in [25], the deformations of seven active and passive strain gauges, installed on each of the LFS layers, were recorded.
The places of installation of the active strain gauges and temperature sensors in the central part of the model are shown in  In  1G f -strain gauge on the tile, separated from the adhesive by a PVC foil, 2G-strain gauge on the tile, covered with adhesive, 3K f -strain gauge on the adhesive, separated from the tile by a PVC foil, 4X f -strain gauge on the XPS, separated from the adhesive by a PVC foil, 5X-strain gauge on the XPS, coated with adhesive, 6K f -strain gauge on the adhesive (from the bottom of the aluminium foil), separated from the XPS by foil, 7K-strain gauge on the adhesive, covered with adhesive, placed transversely to the heating coil.              1Gf-strain gauge on the tile, separated from the adhesive by a PVC foil, 2G-strain gauge on the tile, covered with adhesive, 3Kf-strain gauge on the adhesive, separated from the tile by a PVC foil, 4Xf-strain gauge on the XPS, separated from the adhesive by a PVC foil, 5X-strain gauge on the XPS, coated with adhesive, 6Kf-strain gauge on the adhesive (from the bottom of the aluminium foil), separated from the XPS by foil, 7K-strain gauge on the adhesive, covered with adhesive, placed transversely to the heating coil.
Besides the deformation research, the displacement of the test model under the influence of temperature changes and its own weight were also tested. For this purpose, the DIC-visual digital image correlation system implemented in the Aramis program was used. Figure 8 shows this collaboration and the stand for displacement test. The maximum width of the view field for the model displacement research was approximately 240 mm. The image was placed between the edge of the model and two points at the centre of the test model.  1Gf-strain gauge on the tile, separated from the adhesive by a PVC foil, 2G-strain gauge on the tile, covered with adhesive, 3Kf-strain gauge on the adhesive, separated from the tile by a PVC foil, 4Xf-strain gauge on the XPS, separated from the adhesive by a PVC foil, 5X-strain gauge on the XPS, coated with adhesive, 6Kf-strain gauge on the adhesive (from the bottom of the aluminium foil), separated from the XPS by foil, 7K-strain gauge on the adhesive, covered with adhesive, placed transversely to the heating coil.
Besides the deformation research, the displacement of the test model under the influence of temperature changes and its own weight were also tested. For this purpose, the DIC-visual digital image correlation system implemented in the Aramis program was used. Figure 8 shows this collaboration and the stand for displacement test. The maximum width of the view field for the model displacement research was approximately 240 mm. The image was placed between the edge of the model and two points at the centre of the test model. Besides the deformation research, the displacement of the test model under the influence of temperature changes and its own weight were also tested. For this purpose, the DIC-visual digital image correlation system implemented in the Aramis program was used. Figure 8 shows this collaboration and the stand for displacement test. The maximum width of the view field for the model displacement research was approximately 240 mm. The image was placed between the edge of the model and two points at the centre of the test model.  A very important stage of the layers deformation research in the LFS system, using the strain gauge techniques, was the performance of correction tests. The correction of the initial deformation results is necessary when there are thermal interactions, which was confirmed in the studies [26,27]. For this purpose, the same measurement technique was used as in the investigated initial deformations, which is shown in Figure 9. During the correction of deformations, active strain gauges were placed separately on each LFS layer (not inside of the composite) and subjected to temperature action, and the passive ones were connected to the prepared previously smaller model with dimensions of 20 × 20 cm. During the research correction, the time of the temperature readings on the samples was synchronized with the results of deformations given by the test equipment. A very important stage of the layers deformation research in the LFS system, using the strain gauge techniques, was the performance of correction tests. The correction of the initial deformation results is necessary when there are thermal interactions, which was confirmed in the studies [26,27]. For this purpose, the same measurement technique was used as in the investigated initial deformations, which is shown in Figure 9. During the correction of deformations, active strain gauges were placed separately on each LFS layer (not inside of the composite) and subjected to temperature action, and the passive ones were connected to the prepared previously smaller model with dimensions of 20 × 20 cm.
During the research correction, the time of the temperature readings on the samples was synchronized with the results of deformations given by the test equipment.
A very important stage of the layers deformation research in the LFS system, using the strain gauge techniques, was the performance of correction tests. The correction of the initial deformation results is necessary when there are thermal interactions, which was confirmed in the studies [26,27]. For this purpose, the same measurement technique was used as in the investigated initial deformations, which is shown in Figure 9. During the correction of deformations, active strain gauges were placed separately on each LFS layer (not inside of the composite) and subjected to temperature action, and the passive ones were connected to the prepared previously smaller model with dimensions of 20 × 20 cm. During the research correction, the time of the temperature readings on the samples was synchronized with the results of deformations given by the test equipment.

Results and Discussion of Experimental Methods
The process of research and calculations using the strain gauge technique was precisely described by Karpiesiuk and Chyzy in [25]. They proved that this type of research consists of several processes. Their reason is the temperature variation during the tests. Therefore, reading only the initial results, without their correction, should be treated as an incomplete research cycle. As proved in [25], this correction, especially when dealing with elastic materials, e.g., polyurethanes, gives the best results when the reaction of strain gauges to temperature (apparent strain) is achieved through experimental studies. In this way, we get different apparent strain curves εv. Examples of temperature reactions are shown in Figure 10. These reactions were achieved through additional experimental studies, starting at 23 °C. They were used to correct the initial deformation results by subtracting from the initial results, obtained from the correction.

Results and Discussion of Experimental Methods
The process of research and calculations using the strain gauge technique was precisely described by Karpiesiuk and Chyzy in [25]. They proved that this type of research consists of several processes. Their reason is the temperature variation during the tests. Therefore, reading only the initial results, without their correction, should be treated as an incomplete research cycle. As proved in [25], this correction, especially when dealing with elastic materials, e.g., polyurethanes, gives the best results when the reaction of strain gauges to temperature (apparent strain) is achieved through experimental studies. In this way, we get different apparent strain curves ε v . Examples of temperature reactions are shown in Figure 10. These reactions were achieved through additional experimental studies, starting at 23 • C. They were used to correct the initial deformation results by subtracting from the initial results, obtained from the correction. The theoretical Equation (1) can also be used to correct the deformation. Based on the theoretical Equation (1) and experimental correction tests (Tables 2 and 3), the deformation correction results were prepared, respectively. The analysis of the deformation results obtained computationally and experimentally confirmed that they can be similar (values and signs −/+) only for "rigid" materials-ceramic tiles. This means that  The theoretical Equation (1) can also be used to correct the deformation the theoretical Equation (1) and experimental correction tests (Tables 2 and  formation correction results were prepared, respectively. The analysis of mation results obtained computationally and experimentally confirmed that t similar (values and signs −/+) only for "rigid" materials-ceramic tiles. This m the appropriate decision for LFS, made of elastic polyurethane adhesives, is a only the results of the experimentally obtained correction.
where Ɛv-the temperature reaction of the strain gauge (the temperature corre CuNi44-Konstantan at 20-200 ℃ + Isotan foil (data manufacturer -Tenmex), and C-the thermal expansion of the constituent ma According to Equation (1), the corrections of the strain gauges used at th temperature, e.g., 20 °C, depending on the adopted materials, will take the followi The theoretical Equation (1) can also be used to correct the deformation. Based on the theoretical Equation (1) and experimental correction tests (Tables 2 and 3), the deformation correction results were prepared, respectively. The analysis of the deformation results obtained computationally and experimentally confirmed that they can be similar (values and signs −/+) only for "rigid" materials-ceramic tiles. This means that the appropriate decision for LFS, made of elastic polyurethane adhesives, is acceptation only the results of the experimentally obtained correction.
where ε v -the temperature reaction of the strain gauge (the temperature correction), CuNi44-Konstantan at 20-200 • C + Isotan foil (data from the manufacturer -Tenmex), and α C -the thermal expansion of the constituent material.  According to Equation (1), the corrections of the strain gauges used at the reference temperature, e.g., 20 • C, depending on the adopted materials, will take the following values: Initial deformation results for LFS constituent materials with lamellae are placed in Table 4. These results were then corrected based on experimental tests. The final results are listed in Table 5. The deformations given are for the central zone (the ceramic tile centrally located). Table 4. Results for preliminary deformations of the floor layers in polyurethane adhesive before the correction (average air temperature T i = 23.4 • C, maximum temperature of the adhesive (Force) on the sensor T kl = 40.5 • C.  T kl -adhesive temperature above the insulation (reading from the sensor), T w -interface temperature between the adhesive and ceramic tile, determined by the Equation (2), T po -temperature on the floor.
In one place, the 5X strain gauge on the XPS, coated with adhesive, no deformation correction was made, considering the experimental data as unreliable. The reason for the Materials 2022, 15, 6466 9 of 20 measurement error could be incorrect readings of strain gauges in the places of two-sided to polyurethane adhesion (which were not separated by a PVC foil).
where U 1 -heat transfer coefficient in the adhesives; U 2 -heat transfer coefficient in the ceramic tiles; T kl -adhesive temperature above the thermal insulation (reading from the sensor); T po -temperature on the ceramic tile.
The values and manner of displacement were measured using the digital image correlation (DIC) method on a span of 232 mm and shown in Figure 11. Displacement measurements were made 7000 s after the start of the test, and their average result was 0.209 mm (0.338-0.129 mm). These values were read when the displacements stabilized. The data in Table 5 show that all materials expand under the influence of temperature. Verification of the deformation value and displacement (deflection) should be confirmed by building the FEM calculation model, using the same conditions and places of installation of strain gauges.

Results and Discussion of Experimental Methods
For this part of the research, the "ORCAN" structure analysis system, version 0.98 was used, which was fully implemented at the Bialystok University of Technology. Structural modelling in this system was carried out through the implementation of procedures and algorithms of the Finite Element Method (FEM). The computer implementation was made with the use of C and PASCAL compilers. Figure 12 shows the mapping of the experimental model where the displacement and the deformation on the edges of the central zone were measured. The materials used in this model were precisely described (together with thickness) in the second part of this paper. This model consisted of these materials, starting from the top side: ceramic tiles, Sika BondT8 polyurethane adhesive, aluminium lamella, Sika Force-7710 L100 polyurethane adhesive, and XPS thermal insulation lying freely on the concrete. The distribution of the measuring strain gauges is shown in Figure 13. The joints of C2S1 have been designed between the tiles. For verification of the experiment, the temperature data at 7000 s from Tables 4 and 5 were used: on the external surface of the tile −8.5 °C; on the joint between the ceramic tile and adhesive BondT8 −12.0 °C; and at the interface of adhesive Force and XPS insulation −16.6 °C. The installation temperature was according to Tables 4 and 5, namely To = Ti = 23.4 °C. The model was loaded with self-weight only. The research model was placed freely on the substrate. This substrate was modelled with a so-called "contact zone", which works like a spring. In the computational analysis of this variant, the friction force

Results and Discussion of Experimental Methods
For this part of the research, the "ORCAN" structure analysis system, version 0.98 was used, which was fully implemented at the Bialystok University of Technology. Structural modelling in this system was carried out through the implementation of procedures and algorithms of the Finite Element Method (FEM). The computer implementation was made with the use of C and PASCAL compilers. Figure 12 shows the mapping of the experimental model where the displacement and the deformation on the edges of the central zone were measured. The materials used in this model were precisely described (together with thickness) in the second part of this paper. This model consisted of these materials, starting from the top side: ceramic tiles, Sika BondT8 polyurethane adhesive, aluminium lamella, Sika Force-7710 L100 polyurethane adhesive, and XPS thermal insulation lying freely on the concrete. The distribution of the measuring strain gauges is shown in Figure 13. The joints of C2S1 have been designed between the tiles. For verification of the experiment, the temperature data at 7000 s from Tables 4 and 5 were used: on the external surface of the tile −8.5 • C; on the joint between the ceramic tile and adhesive BondT8 −12.0 • C; and at the interface of adhesive Force and XPS insulation −16.6 • C. The installation temperature was according to Tables 4 and 5, namely T o = T i = 23.4 • C. The model was loaded with self-weight only. The research model was placed freely on the substrate. This substrate was modelled with a so-called "contact zone", which works like a spring. In the computational analysis of this variant, the friction force was omitted. It was assumed that the floor was laid freely on a concrete base.
scribed (together with thickness) in the second part of this paper. This model consisted of these materials, starting from the top side: ceramic tiles, Sika BondT8 polyurethane adhesive, aluminium lamella, Sika Force-7710 L100 polyurethane adhesive, and XPS thermal insulation lying freely on the concrete. The distribution of the measuring strain gauges is shown in Figure 13. The joints of C2S1 have been designed between the tiles. For verification of the experiment, the temperature data at 7000 s from Tables 4 and 5 were used: on the external surface of the tile −8.5 °C; on the joint between the ceramic tile and adhesive BondT8 −12.0 °C; and at the interface of adhesive Force and XPS insulation −16.6 °C. The installation temperature was according to Tables 4 and 5, namely To = Ti = 23.4 °C. The model was loaded with self-weight only. The research model was placed freely on the substrate. This substrate was modelled with a so-called "contact zone", which works like a spring. In the computational analysis of this variant, the friction force was omitted. It was assumed that the floor was laid freely on a concrete base.  The numerical model was built considering the cross-section through the centre of the test system. The plane stress state (PSS) working in a unit thickness of 1.0 m was used. This means that in the direction perpendicular to the separated band, the stresses are close to zero. Zero stresses were assumed in the direction perpendicular to the separated strip, which is a consequence of the lack of friction and other resistances caused, for example, by volumetric resistances related to the limited geometry of the room, or other resistances. The finite elements were rectangular shapes, dimensions 1 × 2 mm. Contact with the substrate was modelled with special one-dimensional spring-type finite elements, in which the stiffness change was used, depending on the direction of internal forces in the spring. The heating pipes' dimensions of 0.3 × 0.3 mm were modelled, as the beam elements with the cross-section of the aluminium coil layer. Horizontal support was applied in the axis of symmetry (the blue arrows in Figures 12 and 13) to stabilize the computational model. The division into finite elements with the temperature distribution, shown in Figure 14. Figure 15 shows the 3D model visualization. The numerical model was built considering the cross-section through the centre of the test system. The plane stress state (PSS) working in a unit thickness of 1.0 m was used. This means that in the direction perpendicular to the separated band, the stresses are close to zero. Zero stresses were assumed in the direction perpendicular to the separated strip, which is a consequence of the lack of friction and other resistances caused, for example, by volumetric resistances related to the limited geometry of the room, or other resistances. The finite elements were rectangular shapes, dimensions 1 × 2 mm. Contact with the substrate was modelled with special one-dimensional spring-type finite elements, in which the stiffness change was used, depending on the direction of internal forces in the spring. The heating pipes' dimensions of 0.3 × 0.3 mm were modelled, as the beam elements with the cross-section of the aluminium coil layer. Horizontal support was applied in the axis of symmetry (the blue arrows in Figures 12 and 13) to stabilize the computational model. The division into finite elements with the temperature distribution, shown in Figure 14. Figure 15 shows the 3D model visualization.
with the substrate was modelled with special one-dimensional spring-type finite elements, in which the stiffness change was used, depending on the direction of internal forces in the spring. The heating pipes' dimensions of 0.3 × 0.3 mm were modelled, as the beam elements with the cross-section of the aluminium coil layer. Horizontal support was applied in the axis of symmetry (the blue arrows in Figures 12 and 13) to stabilize the computational model. The division into finite elements with the temperature distribution, shown in Figure 14. Figure 15 shows the 3D model visualization.  The measurement results are set below (Figures 16-20). Figure 16 shows the method of LFS deflection and displacement from thermal actions obtained through numerical calculations. The displacement and deformations from 7000 s of the experiment should be compared. The displacement at the edge of the model was 2.26 × 10 −4 m. The map of horizontal stresses x is shown in Figure 17. The cross-sections I-I and II-II marked in this drawing pass through the strain gauges located in these places. The map of horizontal deformations is shown in Figures 18-20 the results of deformation in cross-sections I-I and II-II are defined. The deformation of the materials to which the strain gauges are attached is marked in red.   The measurement results are set below (Figures 16-20). Figure 16 shows the method of LFS deflection and displacement from thermal actions obtained through numerical calculations. The displacement and deformations from 7000 s of the experiment should be compared. The displacement at the edge of the model was 2.26 × 10 −4 m. The map of horizontal stresses σ x is shown in Figure 17. The cross-sections I-I and II-II marked in this drawing pass through the strain gauges located in these places. The map of horizontal deformations is shown in Figures 18-20 the results of deformation in cross-sections I-I and II-II are defined. The deformation of the materials to which the strain gauges are attached is marked in red. The measurement results are set below (Figures 16-20). Figure 16 shows the method of LFS deflection and displacement from thermal actions obtained through numerical calculations. The displacement and deformations from 7000 s of the experiment should be compared. The displacement at the edge of the model was 2.26 × 10 −4 m. The map of horizontal stresses x is shown in Figure 17. The cross-sections I-I and II-II marked in this drawing pass through the strain gauges located in these places. The map of horizontal deformations is shown in Figures 18-20 the results of deformation in cross-sections I-I and II-II are defined. The deformation of the materials to which the strain gauges are attached is marked in red.   The measurement results are set below (Figures 16-20). Figure 16 shows the method of LFS deflection and displacement from thermal actions obtained through numerical calculations. The displacement and deformations from 7000 s of the experiment should be compared. The displacement at the edge of the model was 2.26 × 10 −4 m. The map of horizontal stresses x is shown in Figure 17. The cross-sections I-I and II-II marked in this drawing pass through the strain gauges located in these places. The map of horizontal deformations is shown in Figures 18-20 the results of deformation in cross-sections I-I and II-II are defined. The deformation of the materials to which the strain gauges are attached is marked in red.        Table 6 summarizes the results of deformations from experimental tests, comparing them with the results of numerical calculations and comments on them. Strain gauge glued to the XPS, separated from the   Table 6 summarizes the results of deformations from experimental tests, comparing them with the results of numerical calculations and comments on them.   Table 6 summarizes the results of deformations from experimental tests, comparing them with the results of numerical calculations and comments on them.
Relative differences, placed in Table 6, obtained from tests and calculations are not greater than 6.1%-when separating the strain gauges from the material with foils. Larger deviations occur in the place where the strain gauges are not separated from the layer material (point 2G). However, considering Zajac's research thesis [28], this value can be assumed as reliable. The "too large" error occurs only at point 4X f , where the probable cause could be the imprecise sticking of the strain gauge. The displacements between the experimental and the computational version also differ slightly, only by 0.02 mm. The average result-for the tests is 0.205 mm, calculated is 0.226 mm. It can be concluded that small differences in the deformation and displacement of LFS with aluminium lamellae and polyurethane adhesives prove the correctness of the material parameters adopted for calculations, as well as the correct preparation of the research models. Convergent results of the verification of experimental tests and FEM calculations allow to check the stresses and then relate them to the strength of materials used in LFS. For this purpose, numerical calculations with the finite element method were used. A reinforced concrete floor with a span of 6 m was adopted ( Figure 21) with self-weight and imposed load, as well as non-static thermal actions, assumed from the experimental model. An extreme deflection was also assumed of the reinforced concrete ceiling with the value of 3.10 cm, in accordance with the standard [29] obtained after applying a uniformly distributed load of 30 kN/m 2 . The purpose of the numerical calculations was to check whether the stresses of the materials in the lightweight floor, where polyurethane adhesives were used, at various load combinations, including the maximum (according to the standards) ceiling deflection, would not exceed the strength. The assumptions for the calculations were as follows:

•
The lightweight floor model with polyurethane adhesive was repeatedly duplicated up to a ceiling span of 6.00 m.

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The reinforced concrete ceiling was connected to the thermal insulation with C2S1 adhesive.

•
The reinforced concrete ceiling had a 20 cm of thickness.

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The joints were the same as in the experimental model, made from C2S1 adhesive • The gaps, with thickness of 1 mm, between the XPS insulation were made.

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The aluminium foil was modelled separately in PSS.

•
The self-weight, the imposed load of 2 kN/m 2 , and the thermal action were as in the experimental model. Larger deviations occur in the place where the strain gauges are not separated from the layer material (point 2G). However, considering Zajac's research thesis [28], this value can be assumed as reliable. The "too large" error occurs only at point 4Xf, where the probable cause could be the imprecise sticking of the strain gauge. The displacements between the experimental and the computational version also differ slightly, only by 0.02 mm. The average result-for the tests is 0.205 mm, calculated is 0.226 mm. It can be concluded that small differences in the deformation and displacement of LFS with aluminium lamellae and polyurethane adhesives prove the correctness of the material parameters adopted for calculations, as well as the correct preparation of the research models. Convergent results of the verification of experimental tests and FEM calculations allow to check the stresses and then relate them to the strength of materials used in LFS. For this purpose, numerical calculations with the finite element method were used. A reinforced concrete floor with a span of 6 m was adopted ( Figure 21) with self-weight and imposed load, as well as non-static thermal actions, assumed from the experimental model. An extreme deflection was also assumed of the reinforced concrete ceiling with the value of 3.10 cm, in accordance with the standard [29] obtained after applying a uniformly distributed load of 30 kN/m 2 . The purpose of the numerical calculations was to check whether the stresses of the materials in the lightweight floor, where polyurethane adhesives were used, at various load combinations, including the maximum (according to the standards) ceiling deflection, would not exceed the strength. The assumptions for the calculations were as follows: • The maximum deflection 1/200 from the standard [29] (assumed to be 31 mm; Figure  22).

•
The lightweight floor model with polyurethane adhesive was repeatedly duplicated up to a ceiling span of 6.00 m.

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The reinforced concrete ceiling was connected to the thermal insulation with C2S1 adhesive.

•
The reinforced concrete ceiling had a 20 cm of thickness.

•
The joints were the same as in the experimental model, made from C2S1 adhesive • The gaps, with thickness of 1 mm, between the XPS insulation were made.

•
The aluminium foil was modelled separately in PSS.

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The self-weight, the imposed load of 2 kN/m 2 , and the thermal action were as in the experimental model. Figure 23 shows the middle zone with all floor layers and the joints.            The numerical verification, with or without deflections is presented in Table 7, together with comments. There are stress comparisons in selected sections to the maximum horizontal, vertical and tangential strengths of the LFS with aluminium lamellae. The stress in these sections was divided into two variants, T-thermal action without concrete ceiling deflection, T + U-thermal action and imposed load with the maximum standard concrete ceiling deflection. These two loads are separated by the "/" sign. Oth- The numerical verification, with or without deflections is presented in Table 7, together with comments. There are stress comparisons in selected sections to the maximum horizontal, vertical and tangential strengths of the LFS with aluminium lamellae. The stress in these sections was divided into two variants, T-thermal action without concrete ceiling deflection, T + U-thermal action and imposed load with the maximum standard concrete ceiling deflection. These two loads are separated by the "/" sign. Oth- The numerical verification, with or without deflections is presented in Table 7, together with comments. There are stress comparisons in selected sections to the maximum horizontal, vertical and tangential strengths of the LFS with aluminium lamellae. The stress in these sections was divided into two variants, T-thermal action without concrete ceiling deflection, T + U-thermal action and imposed load with the maximum standard concrete ceiling deflection. These two loads are separated by the "/" sign. Other sections IV-VI, included in Table 7 were chosen after analysing the stress maps-with maximum standard deflection and thermal action on the floor, but without imposed loads. This was necessary for complete stress analysis. Additionally, it was noticed that shear stresses at the edges of the floor, which was confirmed by the analytical methods for determining the stresses of glued layers described by da Silva et al. in [30,31] and Adams, Wake [32]. Large stocks of load capacity in connection with the ceiling ⊕-tensile stresses, -compressive stresses, σ ymax -max. detachment stresses, T-thermal action without deflection of the concrete ceiling, T + U-thermal action and imposed load with the maximum deflection of the concrete ceiling.
It is worth noting that there is no risk of chipping the cement joint between the ceramic tiles in LFS with aluminium lamellae made from BondT8 and Force polyurethane adhesives (assuming maximum deflection). It is the opposite situation to LFS without lamellae, reinforced by C2S1 adhesive with fibre mesh, described in [26], where this problem had been observed. Although, the cement joints are between the tiles, the horizontal stresses are close to the load-bearing capacity (σ x = 13.03 MPa < 15.3 MPa). It is concerning when the service loads and maximum standard deflections with thermal action value DT = 16.6 • C (40.0-23.4 • C from Table 5) between the floor and air temperature occur simultaneously.
Besides, there are large stocks of load capacity in each LFS layer with lamellae. Moreover, joining the light floor system with the concrete ceiling using C2S1 cement adhesive, the stress is lower than the load-bearing capacity of this adhesive.
Other calculation simulations, e.g., T + U with maximum deflections but without the imposed load-which are not in Table 7, confirmed that the condition of the load capacity of the floor layers and its adhesive connection with the ceiling were met (the stress was even lower than in simulations from Table 7), namely:

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The maximum compressive stress σ x in the tiles is 9.42 < 240 MPa (when the imposed load was there, the maximum stress was 16.72 MPa) and in the C2S1 adhesive (on the joints I-I) was 4.64 < 15.3 MPa (when the imposed load was there, the maximum stress was 13.03 MPa).

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The maximum tensile stress σ x in the C2S1 adhesive, which connected the concrete ceiling to the XPS thermal insulation, was ⊕ 0.03 < 15.3 MPa (when the imposed load was there, the maximum stress was ⊕ 0.10 MPa).

Conclusions
There is a lot of research in the literature on the efficiency and thermal comfort of LFS and its advantages. Taking this into consideration, the authors of this article went further and undertook to check whether the stresses of individual layers of this type of system are not greater than their strength. If so, they asked whether it can be used in a specific material application without fear of damage? This was the main reason why this type of LFS research and analysis was undertaken.
The experimental studies and computational analyses of LFS with aluminium lamellae justify the specification of the final conclusions. The applications were divided into two thematic groups according to the scope of the work, namely: • conclusions regarding experimental research. • conclusions regarding the numerical model. The results of the conducted research justify its further development, such as: (a) The LFS analysis of non-ceramic floors, e.g., glued floorboards, vinyl floors, wood floors and others, (b) checking the strength of the system with different types and thicknesses of thermal insulation layers, (c) analysis of the mechanical fastening of thermal insulation to the wooden substrate, which may take place in buildings with wooden structures, using various load patterns and thermal impacts.
Finally, to develop guidelines for the design and implementation of LFS in various insulation and flooring variants.